Adaptive radio transceiver with a power amplifier

ABSTRACT

An exemplary embodiment of the present invention described and shown in the specification and drawings is a transceiver with a receiver, a transmitter, a local oscillator (LO) generator, a controller, and a self-testing unit All of these components can be packaged for integration into a single IC including components such as filters and inductors. The controller for adaptive programming and calibration of the receiver, transmitter and LO generator. The self-testing unit generates is used to determine the gain, frequency characteristics, selectivity, noise floor, and distortion behavior of the receiver, transmitter and LO generator. It is emphasized that this abstract is provided to comply with the rules requiring an abstract which will allow a searcher or other reader to quickly ascertain the subject matter of the technical disclosure. It is submitted with the understanding that it will not be used to interpret or limit the scope or the meaning of the claims.

CROSS-REFERENCE TO RELATED APPLICATION

[0001] The present application is a continuation of co-pending patentapplication Ser. No. 09/634,552, filed Aug. 8, 2000, priority of whichis hereby claimed under 35 U.S.C. § 120. The present application alsoclaims priority under 35 U.S.C. § 119(e) to provisional Application No.60/160,806, filed Oct. 21, 1999; Application No. 60/163,487, filed Nov.4, 1999; Application No. 60/163,398, filed Nov. 4, 1999; Application No.60/164,442, filed Nov. 9, 1999; Application No. 60/164,194, filed Nov.9, 1999; Application No. 60/164,314, filed Nov. 9, 1999; Application No.60/165,234, filed Nov. 11, 1999; Application No. 60/165,239, filed Nov.11, 1999; Application No. 60/165,356; filed Nov. 12, 1999; ApplicationNo. 60/165,355, filed Nov. 12, 1999; Application No. 60/172,348, filedDec. 16, 1999; Application No. 60/201,335, filed May 2, 2000;Application No. 60/201,157, filed May 2, 2000; Application No.60/201,179, filed May 2, 2000; Application No. 60/202,997, filed May 2,2000; Application No. 60/201,330, filed May 2, 2000. All theseapplications are expressly incorporated herein by referenced as thoughfully set forth in full.

FIELD OF THE INVENTION

[0002] The present invention relates to telecommunication systems, andin particular, to radio transceiver systems and techniques.

BACKGROUND OF THE INVENTION

[0003] Transceivers are used in wireless communications to transmit andreceive electromagnetic waves in free space. In general, a transceivercomprises three main components: a transmitter, a receiver, and an LOgenerator or frequency synthesizer. The function of the transmitter isto modulate, upconvert, and amplify signals for transmission into freespace. The function of the receiver is to detect signals in the presenceof noise and interference, and provide amplification, downconversion anddemodulation of the detected the signal such that it can be displayed orused in a data processor. The LO generator provides a reference signalto both the transmitter for upconversion and the receiver fordownconversion.

[0004] Transceivers have a wide variety of applications ranging from lowdata rate wireless applications (such as mouse and keyboard) to mediumdata rate Bluetooth and high data rate wireless LAN 802.11 standards.However, due to the high cost, size and power consumption of currentlyavailable transceivers, numerous applications are not being fullycommercialized. A simplified architecture would make a transceiver moreeconomically viable for wider applications and integration with othersystems. The integration of the transceiver into a single integratedcircuit (IC) would be an attractive approach. However, heretofore, theintegration of the transceiver into a single IC has been difficult dueto process variations and mismatches. Accordingly, there is a need foran innovative transceiver architecture that could be implemented on asingle IC, or alternatively, with a minimum number of discrete off-chipcomponents that compensate for process variations and mismatches.

SUMMARY OF THE INVENTION

[0005] In one aspect of the present invention, an amplifier includes aplurality of differential pairs coupled together through a commondifferential output, each differential pair having a current controlinput, and a current switch coupled to the current control input of oneof the differential pairs to selectively switch said one of thedifferential pairs in or out of the amplifier.

[0006] In another aspect of the present invention, a amplifier includesa plurality of amplifying stages each having first and secondtransistors, the first and second transistors each having first, secondand third nodes, the first nodes of the first transistors being coupledtogether and the first nodes of the second transistors being coupledtogether to form a differential output, the second nodes of the firsttransistors being coupled together and the second nodes of the secondtransistors being coupled together to form a differential input, and thethird node of each of the first transistors being coupled to the thirdnode of its respective second transistor to form a current control inputfor each of the amplifying stages, and a current switch coupled to thecurrent control input of one the amplifying stage to switch said one ofthe amplifying stages in or out of the amplifier.

[0007] In yet another aspect of the present invention, an amplifierincludes a plurality of amplifying stages coupled together, each of theamplifying stages having a current control input, and a current switchcoupled to the current control input of one of the amplifying stages toselectively switch said one of the amplifying stages in or out of thecircuit.

[0008] In still another aspect of the present invention, an amplifierincludes a digitally programmable power level and a matching circuitwhich is substantially independent of the programmed power level.

[0009] In a further aspect of the present invention, an amplifierincludes a plurality of amplifying stages coupled together, switchingmeans for switching one of the amplifying stages in or out of theamplifier to program power of the amplifier, and matching means formatching a load coupled to an output of the amplifier, the matchingmeans being substantially independent of the programmed power.

[0010] It is understood that other embodiments of the present inventionwill become readily apparent to those skilled in the art from thefollowing detailed description, wherein it is shown and described onlyembodiments of the invention by way of illustration of the best modescontemplated for carrying out the invention. As will be realized, theinvention is capable of other and different embodiments and its severaldetails are capable of modification in various other respects, allwithout departing from the spirit and scope of the present invention.Accordingly, the drawings and detailed description are to be regarded asillustrative in nature and not as restrictive.

DESCRIPTION OF THE DRAWINGS

[0011] These and other features, aspects, and advantages of the presentinvention will become better understood with regard to the followingdescription, appended claims, and accompanying drawings where:

[0012]FIG. 1 is a block diagram of a transceiver in accordance with anexemplary embodiment of the present invention;

[0013]FIG. 2 is a block diagram of the transceiver blocks including areceiver, transmitter and local oscillator in accordance with anexemplary embodiment of the present invention;

[0014]FIG. 3 is a block diagram of a mixer in accordance with anexemplary embodiment of the present invention;

[0015]FIG. 4 is an electrical diagram of a low noise amplifier inaccordance with an exemplary embodiment of the present invention;

[0016]FIG. 4(a) is an electrical diagram of a low noise amplifier inaccordance with an another exemplary embodiment of the presentinvention;

[0017]FIG. 5 is a block diagram of a four-stage biquad complex bandpassfilter in accordance with an exemplary embodiment of the presentinvention;

[0018]FIG. 6 is an electrical diagram of one biquad stage of the complexbandpass filter in accordance with an exemplary embodiment of thepresent invention;

[0019]FIG. 7 is a graphical depiction of the frequency response on thebiquad stage of FIG. 6 in accordance with an exemplary embodiment of thepresent invention;

[0020]FIG. 8 is an electrical diagram of one possible input circuit forthe biquad stage in accordance with an exemplary embodiment of thepresent invention;

[0021]FIG. 9 is an electrical diagram of another possible input circuitfor the biquad stage in accordance with an exemplary embodiment of thepresent invention;

[0022]FIG. 10 is an electrical diagram of a modified a modified biquadstage of FIG. 6 in accordance with an exemplary embodiment of thepresent invention;

[0023]FIG. 11 is a graphical depiction of the frequency response of themodified biquad stage of FIG. 10 in accordance with an exemplaryembodiment of the present invention;

[0024]FIG. 12(a) is an electrical diagram of a tunable array ofcapacitors in accordance with an exemplary embodiment of the presentinvention;

[0025]FIG. 12(b) is an electrical diagram of ta tunable array ofresistors in accordance with an exemplary embodiment of the presentinvention;

[0026]FIG. 13 is a block diagram of a complex bandpass filter usingpolyphase in accordance with an exemplary embodiment of the presentinvention;

[0027]FIG. 14 is a block diagram of a programmable multiple stageamplifier in accordance with an exemplary embodiment of the presentinvention;

[0028]FIG. 15 is a block diagram of an input and/or output stage for theprogrammable multiple stage amplifier of FIG. 14 in accordance with anexemplary embodiment of the present invention;

[0029]FIG. 16(a) is a block diagram of one core amplifier stage of theprogrammable multiple stage amplifier of FIG. 14 in accordance with anexemplary embodiment of the present invention;

[0030]FIG. 16(b) is a block diagram of a full-wave rectifier of the ofthe programmable multiple stage amplifier of FIG. 14 in accordance withan exemplary embodiment of the present invention;

[0031]FIG. 17(a) is an IF mixer in accordance with an exemplaryembodiment of the present invention;

[0032]FIG. 17(b) is a graphical depiction of a frequency spectrum forthe limited IF clocks into the mixer of FIG. 17(a) in accordance with anexemplary embodiment of the present invention;

[0033]FIG. 17(c) is a graphical depiction of a frequency spectrum forthe IF input into the mixer of FIG. 17(a) in accordance with anexemplary embodiment of the present invention;

[0034]FIG. 17(d) is a graphical depiction of a frequency spectrum forthe output of the mixer of FIG. 17(a) in accordance with an exemplaryembodiment of the present invention;

[0035]FIG. 18 is a clock generator in accordance with an exemplaryembodiment of the present invention;

[0036]FIG. 19(a) is a graphical depiction of a clock signal spectruminput into the clock generator of FIG. 18 in accordance with anexemplary embodiment of the present invention;

[0037]FIG. 19(b) is a graphical depiction of a signal spectrum at theoutput of a two second stage polyphase filter of the clock generator ofFIG. 18 in accordance with an exemplary embodiment of the presentinvention;

[0038]FIG. 19(c) is a graphical depiction of the signal spectrum outputfrom a low pass filter of the clock generator of FIG. 18 in accordancewith an exemplary embodiment of the present invention;

[0039]FIG. 20(a) is a graphical depiction of a signal spectrum at theinput to a polyphase filter in accordance with an exemplary embodimentof the present invention;

[0040]FIG. 20(b) is a graphical depiction of a signal spectrum at theoutput of the polyphase filter in accordance with an exemplaryembodiment of the present invention;

[0041]FIG. 20(c) is a graphical depiction of the signal spectrum outputfrom a low pass filter of the polyphase filter in accordance with anexemplary embodiment of the present invention;

[0042]FIG. 21 is a block diagram of a demodulator in accordance with anexemplary embodiment of the present invention;

[0043]FIG. 22 is a block diagram of a differentiator of the demodulatorof FIG. 21 in accordance with an exemplary embodiment of the presentinvention;

[0044]FIG. 23 is a block diagram of a multiplier of the demodulator ofFIG. 21 in accordance with an exemplary embodiment of the presentinvention;

[0045]FIG. 24 is a block diagram of a peak detector/slicer of thedemodulator of FIG. 21 in accordance with an exemplary embodiment of thepresent invention;

[0046]FIG. 25 is a block diagram of a differential power amplifier inaccordance with an exemplary embodiment of the present invention;

[0047]FIG. 26(a) is a electrical diagram of one bias circuit to theinput and/or output stage of the differential power amplifier of FIG. 25in accordance with an exemplary embodiment of the present invention;

[0048]FIG. 26(b) is an electrical diagram of another bias circuit to theinput and/or output stage of the differential power amplifier of FIG. 25in accordance with an exemplary embodiment of the present invention;

[0049]FIG. 27 is an electrical diagram of a bias circuit for a thecurrent source of the differential power amplifier of FIG. 25 inaccordance with an exemplary embodiment of the present invention;

[0050]FIG. 28 is an electrical diagram of a power control circuit forthe differential power amplifier of FIG. 25 in accordance with anexemplary embodiment of the present invention;

[0051]FIG. 29 is an electrical diagram of a single-ended differentialpower amplifier in accordance with an exemplary embodiment of thepresent invention;

[0052]FIG. 30 is an electrical diagram of digitally programmable CMOSpower amplifier in accordance with an exemplary embodiment of thepresent invention;

[0053]FIG. 31(a) is a block diagram of a local oscillator (LO)architecture in accordance with an exemplary embodiment of the presentinvention;

[0054]FIG. 31(b) is a block diagram of an LO architecture in accordancewith another exemplary embodiment of the present invention;

[0055]FIG. 32 is a block diagram of a LO architecture in accordance withan alternative exemplary embodiment of the present invention;

[0056]FIG. 33 is a block diagram of a LO architecture in accordance withan yet another exemplary embodiment of the present invention;

[0057]FIG. 33(a) is a block diagram of a limiting buffer for the LOarchitecture of FIG. 33 in accordance with an exemplary embodiment ofthe present invention;

[0058]FIG. 34 is a block diagram of a wide tuning range voltagecontrolled oscillator (VCO) in accordance with an exemplary embodimentof the present invention;

[0059]FIG. 35 is an electrical diagram of the wide tuning range VCO ofFIG. 34 in accordance with an exemplary embodiment of the presentinvention;

[0060]FIG. 36(a) is a graphical depiction showing a typical VCO tuningcurve;

[0061]FIG. 36(b) is a graphical depiction of a segmented VCO tuningcurve in accordance with an exemplary embodiment of the presentinvention;

[0062]FIG. 37(a) is a block diagram of a cross-coupled VCO incombination with a frequency divider in accordance with an exemplaryembodiment of the present invention;

[0063]FIG. 37(b) is a block diagram of a VCO in combination with adivider and polyphase circuit in accordance with an exemplary embodimentof the present invention;

[0064]FIG. 38 is a block diagram of a controller in accordance with anexemplary embodiment of the present invention;

[0065]FIG. 39 is an electrical diagram of an RC calibration circuit inaccordance with an exemplary embodiment of the present invention;

[0066]FIG. 40 is a block diagram of an RC calibration circuit usingpolyphase in accordance with an exemplary embodiment of the presentinvention;

[0067]FIG. 41 is an electrical diagram of a capacitor array inaccordance with an exemplary embodiment of the present invention;

[0068]FIG. 42 is an electrical diagram of a bandgap calibration circuitin accordance with an exemplary embodiment of the present invention;

[0069]FIG. 43 is a block diagram of bandgap circuit in accordance withan exemplary embodiment of the present invention;

[0070]FIG. 44 is a electrical diagram of a resistor array in accordancewith an exemplary embodiment of the present invention;

[0071]FIG. 45 is a block diagram of a floating MOS capacitor inaccordance with an exemplary embodiment of the present invention;

[0072]FIG. 46 is an electrical diagram of a duplexing circuit with thepower amplifier on and the low noise amplifier off in accordance with anexemplary embodiment of the present invention; and

[0073]FIG. 47 is an electrical diagram of a duplexing circuit with thelow noise amplifier on and the power amplifier off in accordance with anexemplary embodiment of the present invention.

DETAILED DESCRIPTION

[0074] Exemplary Embodiments of a Transceiver

[0075] In accordance with an exemplary embodiment of the presentinvention, a tranceiver utilizes a combination of frequency planning,circuit design, layout and implementation, differential signal paths,dynamic calibration, and self-tuning to achieve robust performance overprocess variation and interference. This approach allows for the fullintegration of the transceiver onto a single IC for a low cost, lowpower, reliable and more compact solution. This can be achieved by (1)moving external bulky and expensive image reject filters, channel selectfilters, and baluns onto the RF chip; (2) reducing the number ofoff-chip passive elements such as capacitors, inductors, and resistorsby moving them onto the chip; and (3) integrating all the remainingcomponents onto the chip. As those skilled in the art will appreciate,the described exemplary embodiments of the transceiver do not requireintegration into a single IC and may be implemented in a variety of waysincluding discrete hardware components.

[0076] As shown in FIG. 1, a described exemplary embodiment of thetransceiver includes an antenna 8, a switch 9, a receiver 10, atransmitter 12, a local oscillator (LO) generator (also called asynthesizer) 14, a controller 16, and a self-testing unit 18. All ofthese components can be packaged for integration into a single ICincluding components such as filters and inductors.

[0077] The transceiver can operate in either a transmit or receive mode.In the transmit mode, the transmitter 12 is coupled to the antenna 8through the switch 9. The switch 9 provides sufficient isolation toprevent transmitter leakage from desensitizing or damaging the receiver10. In the receive mode, the switch 9 directs signal transmissions fromthe antenna 8 to the receiver 10. The position of the switch 9 can becontrolled by an external device (not shown) such as a computer or anyother processing device known in the art.

[0078] The receiver 10 provides detection of desired signals in thepresence of noise and interference. It should be able extract thedesired signals and amplify it to a level where information contained inthe received transmission can be processed. In the described exemplaryembodiment, the receiver 10 is based on a heterodyne complex (I-Q)architecture with a programmable intermediate frequency (IF). The LOgenerator 14 provides a reference signal to the receiver 10 todownconvert the received transmission to the programmed IF.

[0079] A low IF heterodyne architecture is chosen over a directconversion receiver because of the DC offset problem in directconversion architectures. DC offset in direct conversion architecturesarises from a number of sources including impedance mismatches,variations in threshold voltages due to process variations, and leakagefrom the LO generator to the receiver. With a low IF architecture, ACcoupling between the IF stages can be used to remove the DC offset.

[0080] The transmitter 12 modulates incoming data onto a carrierfrequency. The modulated carrier is upconverted by the reference signalfrom the LO generator 14 and amplified to a sufficient power level forradiation into free space through the antenna 8. The transmitter uses adirect conversion architecture. With this approach only one step ofupconversion is required This leads to a reduction in both circuitcomplexity and power consumption.

[0081] The controller 16 performs two functions. The first functionprovides for adaptive programming of the receiver 10, transmitter 14 andLO generator 16. By way of example, the transceiver can be programmed tohandle various communication standards for local area networks (LAN) andpersonal area networks (PAN) including HomeRF, IEEE 802.11, Bluetooth,or any other wireless standard known in the art. This entailsprogramming the transceiver to handle different modulation schemes anddata rates. The described exemplary embodiment of the transceiver cansupport modulation schemes such as Binary Phase Shift Keying (BPSK),Quadrature Phase ShiftKeying (QPSK), offset quadraturephase shiftkeying(OQPSK), Multiple frequency modulations such as M level frequency shiftkeying (FSK), Continuous Phase Frequency Shift Keying modulation (CFSK),Minimum Shift Keying modulation (MSK), Gaussian filtered FSK modulation(GFSK), and Gaussian filtered Minimum Shift Keying (GMSK),Phase/Amplitude modulation (such as Quadrature Amplitude Modulation(QAM)), orthogonal frequency modulation (such as Orthogonal FrequencyDivision Multiplexing (OFDM)), direct sequence spread spectrum systems,and frequency hopped spread spectrum systems and numerous othermodulation schemes known in the art. Dynamic programming of thetransceiver can also be used to provide optimal operation in thepresence of noise and interference. By way of example, the IF can beprogrammed to avoid interference from an external source.

[0082] The second function provides for adaptive calibration of thereceiver 10, transmitter 14 and LO generator 16. The calibrationfunctionality controls the parameters of the transceiver to account forprocess and temperature variations that impact performance. By way ofexample, resistors can be calibrated within exacting tolerances despiteprocess variations in the chip fabrication process. These exactingtolerances can be maintained in the presence of temperature changes byadaptively fine tuning the calibration of the resistors.

[0083] The controller 16 can be controlled externally by a centralprocessing unit (CPU), a microprocessor, a digital signal processor(DSP), a computer, or any other processing device known in the art. Inthe described exemplary embodiment, a control bus 17 provides two waycommunication between the controller 16 and the external processingdevice (not shown). This communication link can be used to externallyprogram the transceiver parameters for different modulation schemes,data rates and IF operating frequencies. The output of the controller 16is used to adjust the parameters of the transceiver to achieve optimalperformance in the presence of process and temperature variations forthe selected modulation scheme, data rate and IF.

[0084] The self-testing unit 18 generates test signals with differentamplitudes and frequency ranges. The test signals are coupled to thereceiver 10, transmitter 12 and LO generator 14 where they are processedand returned to the self-testing unit 18. The return signals are used todetermine the gain, frequency characteristics, selectivity, noise floor,and distortion behavior of the receiver 10, transmitter 12 and LOgenerator 14. This is accomplished by measuring the strength of thesignals output from the self-testing unit 18 against the returnedsignals over the tested frequency ranges. In an exemplary embodiment ofthe self-testing unit 18, these measurements can be made with differenttransceiver parameters by sweeping the output of the controller 16through its entire calibrating digital range, or alternatively makingmeasurements with the controller output set to a selected few points, byway of example, at the opposite ends of the digital range.

[0085] In the described exemplary embodiment, the self-testing unit 18is in communication with the external processing device (not shown) viathe control bus 17. During self-test, the external processing deviceprovides programming data to both the controller 16 and the self-testingunit 18. The self-testing unit 18 utilizes the programming data used bythe controller 16 to set the parameters of the transceiver to determinethe gain, frequency characteristics, selectivity, noise floor, anddistortion behavior of the receiver 10, transmitter 12 and LO generator14.

[0086]FIG. 2 shows a block diagram of the transceiver in accordance withan embodiment of the invention. The described exemplary embodiment isintegrated into a single IC. For ease of understanding, each componentcoupled to the controller is shown with a “program” designation or a“calibration” designation. These designations indicate whether thecomponent is programmed by the controller or calibrated by thecontroller. In practice, in accordance with the described exemplaryembodiment of the present invention, the components that are programmedreceive the MSBs and the components that are calibrated receive theLSBs. The components requiring both programming and calibration receivethe entire digital output from the controller. As those skilled in theart will appreciate, any number of methodologies may be used to deliverprogramming and calibration information to the individual components. Byway of example, a single controller bus could be used having theprogramming and or calibration data with the appropriate componentaddresses.

[0087] The receiver 10 front end includes a low noise amplifier (LNA) 22which provides high gain with good noise figure performance. Preferably,the gain of the LNA 22 can be set by the controller (not shown) througha “select gain” input to maximize the receivers dynamic range. Thedesirability of dynamic gain control arises from the effect of blockersor interferers which can desensitize the LNA. Conventional filterdesigns at the input of the LNA 22 may serve to sufficiently attenuateundesired signals below a certain power level, however, for higher powerblockers or interferers, the LNA 22 should be operated with low gain.

[0088] The output of the LNA 22 is downconverted to a low IF frequencyby the combination of complex IF mixers 24 and a complex bandpass filter26. More particularly, the output of the LNA 22 is coupled to thecomplex IF mixers 24 which generate a spectrum of frequencies based uponthe sum and difference of the received signal and the RF clocks from theLO generator. The complex bandpass filter passes the complex IF signalwhile rejecting the image of the received signal. The image rejectioncapability of the complex IF mixers 24 in cooperation with the complexbandpass filter 26 eliminates the need for the costly and powerconsuming preselect filter typically required at the input of the LNAfor conventional low IF architectures.

[0089] The output of the complex bandpass filter 26 is coupled to aprogrammable multiple gain stage amplifier 28. The amplifier 28 can bedesigned to be programmable to select between a limiter and an automaticgain control (AGC) feature, depending on the modulation scheme used inthe transceiver. The limiting amplifier can be selected if thetransceiver uses a constant envelope modulation such as FSK AGC can beselected if the modulation is not a constant envelope, such as QAM. Inaddition, the bandwidth of the amplifier 28 can be changed by thecontroller to accommodate various data rates and modulation schemes.

[0090] The output of the amplifier 28 is coupled to a second set ofcomplex IF mixers 30 where it is mixed with the IF clocks from the LOgenerator for the purpose of downconverting the complex IF signal tobaseband. The complex IF mixers 30 not only reject the image of thecomplex IF signal, but also reduces some of the unwanted crossmodulation spurious signals thereby relaxing the filtering requirements.

[0091] The complex baseband signal from the mixers 30 is coupled to aprogrammable passive polyphase filter within a programmable low passfilter 32. The programmable low pass filter 32 further filters outhigher order cross modulation products. The polyphase filter can becentered at four times the IF frequency to notch out one of the majorcross modulation products which results from the multiplication of thethird harmonic of the IF signal with the IF clock After the complexbaseband signal is filtered, it either is passed through ananalog-to-digital (A/D) converter 34 to be digitized or is passed to ananalog demodulator 36. The analog demodulator 36 can be implemented tohandle any number of different modulation schemes by way of example FSK.Embodiments of the present invention with an FSK demodulator uses theA/D converter 36 to sample baseband data with other modulation schemesfor digital demodulation in a digital signal processor (not shown).

[0092] The LO generator 14 provides the infrastructure for frequencyplanning. The LO generator 14 includes an IF clock generator 44 and anRF clock generator 47. The IF clock generator includes an oscillator 38operating at a ratio of the RF signal (f_(OCS)). High stability andaccuracy can be achieved in a number of ways including the use of acrystal oscillator.

[0093] The reference frequency output from the oscillator 38 is coupledto a divider 40. The divider 40 divides the reference signal f_(OSC) bya number L to generate the IF clocks for downconverting the complex IFsignal in the receiver to baseband. A clock generator 41 is positionedat the output of the divider 40 to generate a quadrature sinusoidalsignal from the square wave output of the divider 40. Alternatively, theclock generator 41 can be located in the receiver. The divider 40 may beprogrammed by through the program input This feature allows changes inthe IF frequency to avoid interference from an external source.

[0094] The output of the divider 40 is coupled to the RF clock generator47 where it is further divided by a number n by a second divider 42. Theoutput of the second divider 42 provides a reference frequency to aphase lock loop (PLL) 43. The PLL includes a phase detector 45, a divideby M circuit 46 and a voltage controlled oscillator (VCO) 48. The outputof the VCO 48 is fed back through the divide by M circuit 46 to thephase detector 45 where it is compared with the reference frequency. Thephase detector 45 generates an error signal representative of the phasedifference between the reference frequency and the output of the divideby M circuit 46. The error signal is fed back to the control input ofthe VCO 48 to adjust its output frequency fvco until the VCO 48 locks toa frequency which is a multiple of the reference frequency. The VCO 48may be programmed by setting M via the controller through the programinput to the divide by M circuit 46. The programmability resolution ofthe VCO frequency fvco is set by the reference frequency which also maybe programmed by the controller through the program input of the divider42.

[0095] In the described exemplary embodiment, the VCO frequency issufficiently separated (in frequency) from the RF frequency generated bythe transmitter 12 to prevent VCO pulling and injection lock of the VCO.Transmitter leakage can pull the VCO frequency toward the RF frequencyand actually cause the VCO to lock to the RF signal if their frequenciesare close to each other. The problem is exasperated if the gain andtuning range of the VCO is large. If the frequency of the RF clocks isf_(LO), then the VCO frequency can be defined as: f_(VCO)=Nf_(LO)/(N+1).This methodology is implemented with a divide by N circuit 50 coupled tothe output of the VCO 48 in the PLL 43. The output of the VCO 48 and theoutput of the divide by N circuit 50 are coupled to a complex mixer 52where they are multiplied together to generate the RF clocks. A filter53 can be positioned at the output of the complex mixer to remove theharmonics and any residual mixing images of the RF clocks. The divide byN circuit can be programmable via the controller through the selectinput. For example, if N=2, then f_(VCO)=(⅔)f_(LO), and if N=3, thenf_(VCO)=(¾) f_(LO).

[0096] A VCO frequency set at ⅔ the frequency of the RF clocks workswell in the described exemplary embodiment because the transmitteroutput is sufficiently separated (in frequency) from the VCO frequency.In addition, the frequency of the RF clocks is high enough so that itsharmonics and any residual mixing images such as f_(VCO)×1−(1/N),3f_(VCO)×1+(1/N), and 3f_(VCO)×1−(1/N)) are sufficiently separated (infrequency) from the transmitter output to relax the filteringrequirements of the RF clocks. The filtering requirements do not have tobe sharp because the filter can better distinguish between the harmonicsand the residual images when they are separated infrequency. Programmingthe divide by N circuit 50 also provides for the quadrature outputs ofthe divide by N circuit. Otherwise, with an odd number programmed, theoutputs of the divide by N circuit 50 would not be quadrature. For anodd number, the divider 50 outputs will be differential, but will not be90 degrees out of phase, i.e., will not be I-Q signals.

[0097] In the described exemplary embodiment, the RF clocks aregenerated in the in the LO generator 14. This can be accomplished invarious fashions including, by way of example, either generating the RFclocks in the VCO or using a polyphase circuit to generate the RFclocks. Regardless of the manner in which the RF clocks are generated,the mixer 52 will produce a spectrum of frequencies including the sumand difference frequencies, specifically, f_(VCO)×(1+(1/N)) and itsimage f_(VCO)×(1−(1/N)). To reject the image, the mixer 52 can beconfigured as a double quadrature mixer as depicted in FIG. 3. Thedouble quadrature mixer includes one pair of mixers 55, 57 to generatethe Q-clock and a second pair of mixers 59, 61 to generate the I-clock.The Q-clock mixers utilizes a first mixer 55 to mix the I output of theVCO 48 (see FIG. 2) with the Q output of the divider 40 and a secondmixer 57 to mix the Q output of the VCO with the I output of thedivider. The outputs of the first and second mixers are connectedtogether to generate the Q-clock. Similarly, the I-clock mixers utilizesa first mixer 59 to mix the I output of the divider with the Q output ofthe VCO and a second mixer 61 to mix the Q output of the divider withthe I output of the VCO. The outputs of the first and second mixers areconnected together to generate the I-clock. This technique provides veryaccurate I-Q clocks by combination of quadrature VCO and filtering.Because of the quadrature mixing, the accuracy of the I-Q clocks is notaffected by the VCO inaccuracy, provided that the divide by N circuitgenerates quadrature outputs. This happens for even divide ratios, suchas N=2.

[0098] Optimized performance is achieved through frequency planning andimplemented by programmable dividers in the LO generator to selectdifferent ratios. Based on FIG. 2, all the dependencies of thefrequencies are shown by the following equation:

f _(LO) =f _(RF)−(M×f _(OSC) /nL)(1+1/N)=f _(OSC) /L

[0099] where f_(RF) is frequency of the transmitter output.

[0100] Turning back to FIG. 2, the transmitter 12 includes a complexbuffer 54 for coupling incoming I-Q modulated baseband signals to aprogrammable low-pass filter 56. The low-pass filter 56 can beprogrammed by the controller through the select input. The output of thelow-pass filter 56 is coupled to complex mixers 58. The complex mixers58 mixes the I-Q modulated baseband signals with the RF clocks from theLO generator to directly upconvert the baseband signals to thetransmitting frequency. The upconverted signal is then coupled to anamplifier 60 and eventually a power amplifier (PA) 62 for transmissioninto free space through the antenna. A bandpass filter (not shown) maybe disposed after the PA 62 to filter out unwanted frequencies beforetransmission through the antenna

[0101] In the described exemplary embodiment, the transmitter can beconfigured to minimize spurious transmissions. Spurious transmissions ina direct conversion transmitter are generated mainly because of thenonlinearity of the complex mixers and the DC offsets at the input tothe complex mixers. Accordingly, the complex mixers can be designed tomeet a specified IIP3 (Input Intercept Point for the 3^(rd) Harmonic)for the maximum allowable spurs over the frequency spectrum of thecommunications standard. The DC offsets at the input to the complexmixers can be controlled by the physical size of the transistors.

[0102] In addition, the transmitter can be designed to minimize spurioustransmission outside the frequency spectrum of the communicationsstandard set by the FCC. There are two sources for these spurs: the LOgenerator and the transmitter. These spurs can be are suppressed bymultiple filtering stages in the LO generator and transmitter.Specifically, in the LO generator, due to the complex mixing of the VCOsignal with the output of the divide by N circuit, all the spurs are atleast f_(VCO)/N away from the RF clocks. By setting N to 2, by way ofexample, these unwanted spurs will be sufficiently separated (infrequency) from the transmitted signal and are easily removed byconventional filters in the LO generator and transmitter. Thus, thespurs will be mainly limited to the harmonics of the transmitted signal,which are also sufficiently separated (in frequency) from thetransmitted signal, and therefore, can be rejected with conventionalfiltering techniques. For further reduction in spurs, a dielectricfilter may be placed after the PA in the transmitter.

[0103] 1.0 Receiver

[0104] 1.1 Differential Amplifier

[0105] In exemplary embodiments of the present invention, a differentialamplifier can be used to provide good noise immunity in low noiseapplications. Although the differential amplifiers are described in thecontext of a low noise amplifier (LNA) for a transceiver, those skilledin the art will appreciate that the techniques described are likewisesuitable for various applications requiring good noise immunity.Accordingly, the described exemplary embodiments of an LNA for atransceiver is by way of example only and not by way of limitation.

[0106] 1.1.1 Single-to-Differential LNA

[0107] The described LNA can be integrated into a single chiptransceiver or used in other low noise applications. In the case oftransceiver chip integration, the LNA should be relatively insensitiveto the substrate noise or coupling noise from other transceivercircuits. This can be achieved with a single-to-differential LNA. Thesingle-ended input provides an interface with an off-chip single-endedantenna. The differential output provides good noise immunity due to itscommon mode rejection.

[0108]FIG. 4 shows a schematic of a single-to-differential amplifierhaving two identical cascode stages that are driven by the samesingle-ended input 64. The input 64 is coupled to a T-network having twoseries capacitors 82, 84 and a shunt inductor 72. The first stageincludes a pair of transistors 74, 78 connected between the shuntinductor 72 and a DC power source via an inductor 68. The second stageincludes a complimentary pair of transistors 76, 80 connected betweenground and the DC power source via an inductor 70. The gate of the oneof the transistors 80 in the second stage is connected to the output ofthe T-network at the capacitor 84. A bias current is applied to the gateof each transistor.

[0109] This configuration provides an input that is well matched withthe antenna because the parallel connection of the T-network with thesource of the transistor 78 transforms the 1/gm (transconductance) ofthe transistor to a resistance (preferably 50 ohms to match theantenna). By adjusting the values of T-network components, the matchingcircuit can be tuned for different frequencies and source impedances.The input capacitor 82 of the T-network further provides decouplingbetween the antenna and the amplifier.

[0110] For DC biasing purposes, the shunt inductor 72 provides a shortcircuit to ground allowing both stages of the amplifier to operate atthe same DC drain current. The output capacitor 84 provides DC isolationbetween the gate bias applied to the transistor 80 of the second stageand the source 82 of the transistor 78 in the first stage.

[0111] In operation, a signal applied to the input of the amplifier iscoupled to both the source 82 of the transistor 78 of the first stageand the gate 83 of the transistor 80 of the second stage. This causesthe gain of each stage to vary inversely to one another. As a result,the signal voltage applied to the input of the amplifier is converted toa signal current with the signal current in the first stage beinginverted from the signal current in the second stage. Moreover, the twostages will generate the same gain because the gm of the transistorsshould be the same, and therefore, the total gain of the amplifier istwice as much as conventional single-to-differential amplifiers.

[0112] 1.1.2 Differential LNA

[0113] A differential LNA can also be used to provide good noiseimmunity in low noise applications, such as the described exemplaryembodiment of the transceiver. In FIG. 4(a), an exemplary differentialLNA is shown having a cascode differential pair with inductivedegeneration. In the described exemplary embodiment, the differentialLNA can be integrated into a single chip transceiver or used in othersimilar applications.

[0114] In the case of transceiver chip integration, an off chip coupler(not shown) can be used to split the single-ended output from theantenna into a differential output with each output being 180° out ofphase. The LNA input can be matched to the coupler, i.e., a 50 ohmsource, by LC circuits. A shunt capacitor 463 in combination with aseries inductor 465 provides a matching circuit for one output of thecoupler, and a shunt capacitor 467 in combination with a series inductor469 provides a matching circuit for the other output of the coupler. At2.4 GHz., each LC circuit may be replaced by a shunt capacitor andtransmission line. In the described exemplary embodiment, the LCcircuits are off-chip for improved noise figure performance.Alternatively, the LC circuits could be integrated on chip. However, dueto the high loss of on chip inductors, the noise figure, as well asgain, could suffer.

[0115] The differential output of the coupler is connected to adifferential input of the LNA via the LC matching circuits. Thedifferential input includes a pair of input FET transistors 471, 473with inductive degeneration. This is achieved with an on chip sourceinductor 475 connected between the input transistor 471 and ground, anda second on chip source inductor 479 connected between the inputtransistor 473 and ground. The on chip inductive degeneration provides apredominantly resistive input impedance. In addition, the FET noisecontribution at the operating frequency is reduced.

[0116] The outputs of the input transistors 471, 473 are coupled to acascode stage implemented with a pair of transistors 481, 486,respectively. The cascode stage provides isolation between the LNA inputand its output. This methodology improves stability, and reduces theeffect of the output load on the LNA input matching circuits. The gatesof the cascode transistors 481, 486 are biased at the supply voltage bya resistor 488. The resistor 488 reduces instability that mightotherwise be caused by parasitic inductances at the gates of thecascoded transistors 481, 486. Since the described exemplary embodimentof the LNA uses a differential architecture, the resistor does notcontribute noise to the LNA output.

[0117] The output of cascoded transistor 481 is coupled to the supplyvoltage through a first inductor 490. The output of the cascodedctransistor 486 is coupled to the supply voltage through a secondinductor 492. The LNA is tuned to the operating frequency by the outputinductors 490, 492. More particularly, these inductors 490, 492 resonatewith the LNA output parasitic capacitance, and the input capacitance ofthe next state (not shown). Embodiments of the present inventionintegrated into a single integrated circuit do not require a matchingnetwork at the LNA output.

[0118] The gain of the LNA can be digitally controlled. This is achievedby introducing a switchable resistor in parallel with each of the outputinductors. In the described exemplary embodiment, a series resistor 494and switch 496 is connected in parallel with the output inductor 490,and a second series resistor 498 and switch 500 is connected in parallelwith the output inductor 492. The switches can be FET transistors or anyother similar switching devices known in the art. In the low gain mode,each resistor 494, 498 is connected in parallel with its respectiveoutput inductor 490, 492, which in turn, reduces the quality factor ofeach output inductor, and as a consequence the LNA gain. In the highgain mode, the resistors 494, 498 are switched out of the LNA outputcircuit by their respective switches 496, 500.

[0119] 1.2 A Complex Filter

[0120] In an exemplary embodiment of the present invention, aprogrammable/tunable complex filter is used to provide frequencyplanning, agility, and noise immunity. This is achieved with variablecomponents to adjust the frequency characteristics of the complexfilter. Although the complex filter is described in the context of atransceiver, those skilled in the art will appreciate that thetechniques described are likewise suitable for various applicationsrequiring frequency agility or good noise immunity. Accordingly, thedescribed exemplary embodiment for a complex filter in a transceiver isby way of example only and not by way of limitation.

[0121] The described complex filter can be integrated into a single chiptransceiver or used in other low noise applications. In the case oftransceiver chip integration, the off-chip filters used for imagerejection and channel selection can be eliminated. A low-IF receiverarchitecture enables the channel-select feature to be integrated intothe on-chip filter. However, if the IF lies within the bandwidth of thereceived signal, e.g. less than 80 MHz in the Bluetooth standard, theon-chip filter should be a complex filter (which in combination with thecomplex mixers) can suppress the image signal. Thus, either a passive oran active complex filter with channel select capability should be used.Although a passive complex filter does not dissipate any power byitself, it is lossy, and loads the previous stage significantly. Thus,an active complex filter with channel select capability is preferred.The channel select feature of the active complex filter can achievecomparable performance to conventional band-pass channel-select filtersin terms of noise figure, linearity, and power consumption

[0122] The described exemplary embodiment of the complex filteraccommodates several functions in the receiver signal path: it selectsthe desired channel, rejects the image signal which lies inside the databand of the received signal due to its asymmetric frequency response,and serves as a programmable gain amplifier (PGA). Moreover, the complexfilter center frequency and its bandwidth can be programed and tuned.These capabilities facilitate a robust receiver in a wirelessenvironment, where large interferers may saturate the receiver ordegrade the signal-to-noise ratio at the demodulator input. Theattenuation of the received signal at certain frequencies can also beenhanced by introducing zeros in the complex filter.

[0123] 1.2.1 Cascaded Biquads

[0124] An exemplary embodiment of the complex filter includes a cascadeof biquads. Each biquad comprises a 2′nd order bandpass filter. Thetotal order of the filter is the sum of orders of the cascaded biquads.The order of the filter can be programmable. By way of example, fourcascaded biquads 83, 85, 87, 89 can be used with each of the cascadedbiquads having an individually controlled bypass switch. Referring toFIG. 5, a bypass switch 91 is connected across the input stage biquad83. Similarly, a bypass switch 93 is connected across the second stagebiquad 85, a bypass switch 95 is connected across the third stage biquad87, and a bypass switch 97 is connected across the output stage biquad.With this configuration, the order of the filter can be programmed bybypassing one or more biquads. A biquad that is bypassed contributes azero order to the filter.

[0125] In the described exemplary embodiment, the bypass switches areoperated in accordance with the output from the controller 16 (see FIG.2). An 8′th order filter can be constructed by opening the bypassswitches 91, 93, 95, 97 via the digital signal from the controlleroutput. The complex filter can be reduced to a 6′th order filter byclosing the bypass switch 97 to effectively remove the output stagebiquad from the complex filter. Similarly, the complex filter can bereduced to a 4′th order filter by closing bypass switches 95, 97effectively removing the third stage biquad and output stage biquad. A2′nd order filter can be created by closing bypass switches 93, 95, 97effectively removing all biquads with the exception of the input stagefrom the circuit.

[0126] 1.2.1.1 The Poles of a Biquad Stage

[0127]FIG. 6 shows an exemplary embodiment of a biquad stage of thecomplex filter. The biquad stage includes two first orderresistor-capacitor (RC) filters each being configured with adifferential operational amplifier 94, 96, respectively. The firstdifferential operational amplifier 94 includes two negative feedbackloops, one between each differential output and its respectivedifferential input. Each feedback loop includes a parallel RC circuit(98, 106), (108, 100), respectively. Similarly, the second differentialoperational amplifier 96 includes two negative feedback loops, onebetween each differential output and its respective differential input.Each feedback loop includes a parallel RC circuit (102-110), (112-104),respectively. This topology is highly linear, and therefore, should notdegrade the overall IIP3 of the receiver. The RC values determine thepole of the biquad stage.

[0128] The differential inputs of the biquad stage are coupled to theirrespective differential operational amplifiers through input resistors114, 116, 118, 120. The input resistors in combination with theirrespective feedback resistors set the gain of the biquad stage.

[0129] Preferably, some or all of the resistors and capacitors valuescan programmable and can be changed dynamically by the controller Thismethodology provides a frequency agile biquad stage.

[0130] The two first order RC filters are cross coupled by resistors 86,88, 90, 92. By cross-coupling between the two filters, a complexresponse can be achieved, that is, the frequency response at thenegative and positive frequencies will be different. This is in contrastto a real-domain filter, which requires the response to be symmetric atboth positive and the negative frequencies. This feature is usefulbecause the negative frequency response corresponds to the image signal.Thus, the biquad stage selects the desired channel, whereas the imagesignal, which lies at the negative frequency is attenuated.

[0131] For the resistor values shown in FIG. 6, the biquad stage outputsare: $\begin{matrix}{{V_{OI} = {A\frac{{\left( {1 + {j\quad {RC}\quad \omega}} \right)V_{II}} + {2{QV}_{IQ}}}{\left( {1 + {j\quad {RC}\quad \omega}} \right)^{2} + {4Q^{2}}}}}{and}} & (1) \\{V_{OQ} = {A\frac{{{- 2}{QV}_{II}} + {\left( {1 + {j\quad {RC}\quad \omega}} \right)V_{IQ}}}{\left( {1 + {j\quad {RC}\quad \omega}} \right)^{2} + {4Q^{2}}}}} & (2)\end{matrix}$

[0132]FIG. 7 shows the frequency response for the complex biquad filter.

[0133] After the received signal is downconverted, the desired channelin the I path lags the one in the Q path, that is, V_(n)=−jV_(1Q), andtherefore: $\begin{matrix}{{H({j\omega})} = {{\frac{V_{o}}{V_{l}}\left( {j\quad \omega} \right)} = \frac{A}{1 + {j\quad {RC}\quad \omega} - {j\quad 2Q}}}} & (3)\end{matrix}$

[0134] This shows a passband gain of A 122 at a center frequency of2Q/RC 124, with a 3-dB bandwidth of 2RC 126. Thus, the quality factor ofthe second-order stage will be Q. For the image signal however, thesignal at the I branch leads, and as a result: $\begin{matrix}{{H\left( {j\quad \omega} \right)} = \frac{A}{1 + {j\quad {RC}\quad \omega} + {j\quad 2Q}}} & (4)\end{matrix}$

[0135] which shows that the image located at 2Q/RC is rejected by$\frac{1}{\sqrt{\left( {1 + {\left( {4 \cdot Q} \right)2}} \right.}}.$

[0136] Therefore, the biquad stage has an asymmetric frequency response,that is, the may be assigned to positive frequencies, whereas the imageis attributed to negative frequencies. In general, the frequencyresponse of the biquad stage is obtained by applying the followingcomplex-domain transformation to a normalized real-domain lowpassfilter: $\begin{matrix}{{j\quad \omega} - \frac{j\left( {\omega - \omega_{0}} \right)}{BW}} & (5)\end{matrix}$

[0137] where ω₀ is the bandpass (BP) center frequency, and BW is thelowpass (LP) equivalent bandwidth, equal to half of the bandpass filterbandwidth. For instance, for a second-order biquad stage (as shown inFIG. 6), ω₀=2Q/RC, and BW=1/RC. The biquad stage is designed by findingits LP equivalent frequency response using equation (5). Once the LPpoles are known, the BP poles are calculated based on equation (5).Assume that the LP equivalent has n poles, and P_(i,LP)=αi+jβ_(i) is theith pole. From equation (5), the BP pole will be:

P _(i,BP) =BW·P _(i,LP) +jω ₀=α_(i) ·BW+j(ω₀ +β _(i) ·BW)  (6)

[0138] The complex filter is realized by cascading n biquad stages.Therefore, similar to real-domain bandpass filters, an nth order complexfilter uses 2×n integrators. Based on equation (3), each biquad stagehas a pole equal to −1/RC+j2Q/RC. Thus: $\begin{matrix}{{{\alpha_{i} \cdot {BW}} = \frac{- 1}{RC}}{and}} & (7) \\{{\omega_{o} + {\beta_{i} \cdot {BW}}} = \frac{2Q}{RC}} & (8)\end{matrix}$

[0139] Since the LP equivalent poles are located in the left-half plane,a_(i) is always negative. The above equations set the value of Q and RCin each stage. The gain of each biquad stage can be adjusted based onthe desired gain in the complex filter, and noise-linearity trade-off:increasing the gain of one biquad stage lowers the noise contributed bythe following biquad stages, but it also degrades the linearity of thecomplex filter.

[0140] In addition to image rejection, the complex frequencytransformation of the biquad stage (equation (5)) provides for itsfrequency response to be symmetric around its center frequency as shownin FIG. 7. This is in contrast to regular bandpass filters which use thefollowing real-domain transformation: $\begin{matrix}{{j\quad \omega} - \frac{j\left( {\omega^{2} - \omega_{0}^{2}} \right)}{{BW} \cdot \omega}} & (9)\end{matrix}$

[0141] This symmetric response in the biquad stage ensures a uniformgroup delay across the data band.

[0142] 1.2.1.2 The Zeros of a Biquad Stage

[0143] The described exemplary embodiment of the biquad stage can bemodified to obtain a sharper rejection or notch at an undesired signalat a specific frequency. This can be achieved in the biquad stage byadding zeros. Assume that the input resistors at the biquad input (R_(i)114 in FIG. 6) is replaced with an admittance Y_(i). For the receivedsignal, the frequency response of the biquad stage will be equal to:$\begin{matrix}{{H({j\omega})} = \frac{R \cdot Y_{i}}{1 + {j\quad {RC}\quad \omega} - {j\quad 2Q}}} & (10)\end{matrix}$

[0144]FIG. 8 shows Yi having resistor R_(z) 128 and capacitor C_(z) 130.

[0145] In order to have a zero located at jω axis in the frequencyresponse, Y_(i) should contain a term such as 1−ω/ω_(z). If Y_(i) issimply made of a resistor R_(z) in parallel with a capacitor C_(z), thenthe input admittance will be equal to: $\begin{matrix}{Y_{i} = {\frac{1}{R_{z}} + {{j\omega}\quad C_{z}}}} & (11)\end{matrix}$

[0146] which is not desirable, since the zero will be in the left-halfplane, rather than the j ω axis.

[0147]FIG. 9 shows Yi with the capacitor C_(z) 132 connected to the Qinput 134 and the resistor R_(z) connected to the I input 136. Now thecurrent I will be equal to: $\begin{matrix}{I = {\frac{V}{R_{z}} + {j\quad C_{z}\quad {\omega \cdot \left( {j\quad V} \right)}}}} & (12)\end{matrix}$

[0148] Therefore, the input admittance will be equal to: $\begin{matrix}{Y_{i} = {\frac{1}{V} = {\frac{1}{R_{z}} - {C_{z}\omega}}}} & (13)\end{matrix}$

[0149] which indicates that the filter will have a zero equal to1/R_(z)C_(z) at the jω axis.

[0150]FIG. 10 shows a single biquad stage modified to have a zero at thejω axis. The biquad stage includes capacitors 138, 140, 142, 144. Thecombination of capacitors 138, 140, 142, 148 and resistors 116, 118determines a complex zero with respect to the center frequency. Thetransfer function for the received signal will be: $\begin{matrix}{{H\left( {j\quad \omega} \right)} = {A\quad \frac{1 - {\frac{{RC}_{z}}{A}\omega}}{1 + {{jRC}\quad \omega} - {j2Q}}}} & (14)\end{matrix}$

[0151] Equation (14) is analogous to equation (3), with the differencethat now a zero at A/RC_(z) is added to the biquad stage of the complexfilter. By knowing the LP equivalent characteristics of the biquadstage, the poles are calculated based on equation (6). The value of Qand RC in each biquad stage is designed by using equation (7) andequation (8). If the normalized LP zeros are at ±ω_(z,LP), then thebiquad stage should be realized with two biquad stages cascoded, and thefrequency of zeros in the biquad stages will be (equation (5)):

ω_(z/,2)=ω₀±ω_(z,LP) ·BW  (15)

[0152] If the differential I and Q inputs connected to the zerocapacitors are switched, the biquad stage will have zeros at negativefrequencies (image response). This property may be exploited to notchthe image signal.

[0153] 1.2.1.3 Tunability and Programmability

[0154] In addition to channel selection and image rejection, thedescribed exemplary embodiment of the complex filter can providevariable gain, bandwidth, and center frequency. In addition, anautomatic tuning loop can be implemented to adjust the center frequency.These features result in a high quality receiver which can dynamicallysupport different communication standards, modulation schemes and datarates.

[0155] By changing the gain of the biquad stages, the complex filter canperform as a PGA in the signal path of the receiver. This assures thatthe output swing of the complex filter remains constant when thereceiver input signal changes. Moreover, adaptivity is achieved throughdynamic programming of the bandwidth and center frequency. By way ofexample, when the receive environment is less noisy, the transmitter mayswitch to a higher data rate, and the bandwidth of the complex filtershould increase proportionally. The center frequency, on the other hand,may be changed to increase the receiver immunity to blockers and otherinterferers.

[0156] The center frequency of each biquad stage is equal to 2Q/RC. Thequality factor, Q, is precisely set, since it is determined by the ratioof two resistors (R_(f) and R_(c) in FIG. 10), which can be accuratelyestablished when the resistors are implemented on-chip. However, the RCproduct varies by temperature and process variations, and therefore, maybe compensated by automatic tuning methods.

[0157] Referring to FIG. 12(a), each capacitor can be implemented with acapacitor 148 connected in parallel with a number of switchablecapacitors 150, 152, 154, 156. The capacitance, and thereby the centerfrequency of the complex filter, can be varied by selectively switchingin or out the capacitors based on a four-bit binary code. Each bit isused to switch one of the parallel capacitors from the circuit In thedescribed exemplary embodiment, the capacitor 148 provides acapacitanceof C_(u)/2. Capacitor 150 provides acapacitance of C_(u)/2. Capacitor152 provides a capacitance of C_(u)/4. Capacitor 154 provides acapacitance of C_(u)/8. Capacitor 156 provides a capacitance ofC_(u)/16. This provides ±50% tuning range with ±3% tuning accuracy. Dueto discrete nature of the tuning scheme, there may be some error in thecenter frequency (±1/(2×2^(n)) for n-bit array). This inaccuracy can betolerated with proper design.

[0158] Referring to FIG. 12(b), each resistor can be implemented with aseries of switchable resistors 158, 160, 162, 164, 166. Resistor 166provides a resistance of R_(u). Resistor 164 provides a resistance of 2R_(u). Resistor 162 provides a resistance of 4 R_(u). Resistor 160provides a resistance of 8 R_(u). Resistor 158 provides a resistance of16 R_(u). In the described exemplary embodiment, the resistance can bevaried between R_(u) and 31×R_(u) in incremental steps equal to R_(u) byselectively bypassing the resistor based on a five-bit binary code.

[0159] The center frequency of the complex filter can be adjusted bysetting 1/R_(u)C_(u) equal to a reference frequency generated, by way ofexample, the crystal oscillator in the controller. The filter isautomatically tuned by monotonic successive approximation as describedin detail in Section 4.0 herein. Once the value of R_(u)C_(u) is set,the complex filter characteristics depends only on four-bit code for thecapacitors and the four-bit code for the resistors. For example, assumethat the value of the resistors in the biquad stage of FIG. 6 is asfollowing: R_(i)=n_(A)R_(u), R_(f)=n_(Q)R_(u), and Rc=n_(Q)R_(u).Likewise, assume that C=n_(C)C_(u), where n_(C) is a constant, and that1/R_(u)C_(u)=ω_(u). The value of ω_(u) is set to a reference crystal bya successive approximation feedback loop. The filter frequency responsefor the received signal will be: $\begin{matrix}{{H\left( {j\quad \omega} \right)} = \frac{\frac{n_{F}}{n_{A}}}{1 + {{jn}_{c}n_{F}R_{u}C_{u}\omega} - {j\quad \frac{n_{F}}{n_{Q}}}}} & (16)\end{matrix}$

[0160] Therefore, the biquad stage gain (A), center frequency (ω₀), andbandwidth (BW) will be equal to: $\begin{matrix}{A = \frac{n_{F}}{n_{A}}} & (17) \\{\omega_{0} = {\frac{1}{n_{C}n_{Q}} \cdot \omega_{u}}} & (18) \\{{BW} = {\frac{1}{n_{C}n_{F}} \cdot \omega_{u}}} & (19)\end{matrix}$

[0161] The above equations show that the characteristics of the biquadstage is independently programmed by varying n_(A), n_(F), and n^(Q).For instance, by setting n_(F), the gain of the biquad stage changesfrom n_(F)/31 to n_(f) by changing n_(A) from 1 to 31.

[0162] 1.2.2 I-Q Monolithic Bandpass Filter

[0163] Alternatively, a low power I-Q monolithic bandpass filter can beused for the complex filter of the described exemplary embodiment of thepresent invention. The I-Q monolithic bandpass filter is useful forshort-range communication applications. It also provides low powermonolithic bandpass filtering for high data rates such as Bluetooth andHomeRF applications. The I-Q monolithic bandpass filter can be fullyincorporated in monolithic channel select filters for 1-MHz data rates.

[0164]FIG. 13 is a block diagram of the I-Q monolithic bandpass filterin accordance with an embodiment of the present invention. The I-Qmonolithic bandpass filter includes a cascode of selectively intertwinedbiquads 168 and polyphase circuits 170. The biquads can be the same asthe biquads described in Section 1.2.1 herein, or any other biquadsknown in the art. Similarly, the polyphase circuits can also be anyconventional polyphase circuits known in the art. The biquad circuitscan be 2′nd order lowpass filters, which in conjunction with thepolyphase circuits, exhibit a 1-MHz bandwidth bandpass filter with morethan 45 dB rejection for all frequencies beyond 2 MHz away from thecenter of the band. The number of biquads determines the order of theI-Q monolithic bandpass filter. The polyphase filters are for widerbandwidth and image rejection. The number of polyphase filtersdetermines the number of zeros in the frequency response of the I-Qmonolithic bandpass filter.

[0165] In the described embodiment, an 8′th order Butterworth filter isimplemented in conjunction with selective side band filtering ofpolyphase circuits to create a low IF I-Q monolithic bandpass filter.The described embodiment of the I-Q monolithic bandpass filter does notsuffer excessive group delay despite large bandwidth. The input IP3 canbe better than 5 dBm with a gain of more than 20 dB and the noise figurecan be less than 40 dB. In fully integrated embodiments of the presentinvention, the I-Q monolithic bandpass filter can have on chip tuningcapability to adjust for process, temperature and frequency variations.

[0166] 1.3 Programmable Multiple Gain Amplifier

[0167] In one exemplary embodiment of the present invention, aprogrammable multiple gain amplifier is used in the receiver pathbetween the complex filter and the complex IF mixer (see FIG. 2). Theprogrammable multiple gain amplifier can be designed to be programmableto select between a limiter and an AGC feature. The programmablemultiple gain amplifier, when operating as a limiter provides a maximumgain for frequency modulation applications. The programmable multiplegain amplifier, operating as an AGC, can be used for applicationsutilizing amplitude modulation.

[0168]FIG. 14 shows a block diagram of an exemplary embodiment of theprogrammable multiple gain amplifier with an RSSI output. The RSSIoutput provides an indication of the strength of the IF signal. Theprogrammable multiple gain amplifier includes three types of amplifiers.The input buffer is shown as a type I amplifier 900 and the type IIIamplifier 904 serves as the output buffer. The core amplifier is shownas a direct-coupled cascade of seven differential amplifiers 930, 931,932, 933, 934, 935, 936. The core amplifier includes seven bypassswitches 930′, 931′, 932′, 933′, 934′, 935′, 936′, one bypass switchconnected across each differential amplifier. The bypass switchesprovide programmable gain under control of the controller (see FIG. 2).

[0169] When the programmable gain amplifier is operating as a limiter,all the bypass switches will be opened by the controller. Conversely,when the programmable gain amplifier is operating in the AGC mode, theoutput gain of the core amplifier will be varied by controlling thebypass switch positions to prevent saturation of the core amplifier bylarge signals. In the described exemplary embodiment, the RSSI signal isfed back to control the bypass switch positions through a digital AGCloop in the external processing device. The AGC loop providesinformation to the controller 16 via the control bus 17 regarding theoptimum gain reduction (see FIG. 2). The controller translates theinformation from the external processing device into a digital signalfor controlling the bypass switch positions of the core amplifieraccordingly. The larger the RSSI signal, the greater the gain reductionof the core amplifier will be and the more bypass switches that will beclosed by the controller.

[0170] In one embodiment of the programmable gain amplifier, the type Iand type III amplifiers can be the same. FIG. 15 shows one possibleconstruction of these amplifiers. In this configuration, transistors952, 954 provide amplification of the differential input signal. Thedifferential input signal is fed to the gates of transistor amplifiers952, 954, and the amplified differential output signal is taken from thedrains. The gain of the transistor amplifiers 952, 954 is set by loadresistors 956, 958. Transistors 960, 962 provide a constant currentsource for the transistor amplifiers 952, 954. The load resistors 956,958, connected between the drain of their respective transistoramplifiers 952, 954 and a common gate connection of transistors 960,962, provides a bias current source to common mode feedback.

[0171] Turning back to FIG. 14, the type II core amplifier 902 includesa direct-coupled cascade of seven differential amplifiers 930, 931, 932,933, 934, 935, 936, each with a voltage gain, by way of example, 12 dB.The voltage at the output of each differential amplifier 930, 931, 932,933, 934, 935, 936 is coupled to a rectifier 937, 938, 939, 940, 941,942, 943, 944, respectively. The outputs of the rectifiers are connectedto ground through a common resistor 945. The summation of the currentsfrom each of the rectifiers flowing through the common resistor providesa successive logarithmic approximation of the input IF voltage. With a12 dB gain per each differential amplifier, a total cascaded gain of 84dB is obtained. As those skilled in the art will appreciate, any numberof differential amplifiers, each with the same or different gain, may beemployed.

[0172] The input dynamic range of an RSSI is explained using thefollowing derivation. Throughout this section, assume each rectifier hasan ideal square law characteristic and its transfer function is:

y=β² V ² _(in)  (20)

[0173] Now, assume that S is the maximum input range of one differentialamplifier and rectifier combination, whichever is smaller. This isdetermined with the lowest of the two values V_(i) and V_(L) that arethe maximum input range of each differential amplifier, and the maximuminput range of the rectifier, respectively.

S=min(V_(i) ,V _(L))  (21)

[0174] Therefore, the RSSI maximum input level is S, and the ideal RSSIminimum input level is S/A^(n), where A is the gain of each differentialamplifier and n is the number of the differential amplifiers. Thus, theideal dynamic range is calculated as follows: $\begin{matrix}{{{Ideal}\quad {Dynamic}\quad {Range}} = {{20\log \quad \frac{S}{\frac{S}{A^{n}}}20\log \quad A^{n}} = {20(n)\log \quad A}}} & (22)\end{matrix}$

[0175] However, in the case of a large amount of gain, the input levelwill be limited with the input noise and the dynamic range will also belimited to: $\begin{matrix}{{{DynamicRange} = {20\log \quad \frac{S}{\sqrt{\sigma_{n}}}}}{\sqrt{\sigma_{n}} = {{total}\quad {noise}\quad {rms}}}\text{}{\sigma_{n} = {({BW}) \times {Noise}\quad {Factor}}}} & (23)\end{matrix}$

[0176] If each differential amplifier has the same input dynamic rangeV_(L) and each full-wave rectifier has similar input dynamic rangeV_(i), then the dynamic range of the logarithmic differential amplifierand the total RSSI circuitry are the same.

[0177] The logarithmic approximations are provided by piecewise linearsummation of the rectified output of each differential amplifier. Thisis done by segmentation of the input voltage by the power of 1/A.Successively, each differential amplifier will reach the limiting pointas the input signal grows by the power of A. Assuming each rectifier ismodeled as shown in equation (20), the logarithmic approximation ismodeled as following:

[0178] For an input being in the following range: $\begin{matrix}{\frac{S}{A^{n - m}} < V_{in} < \frac{S}{A^{n - m - 1}}} & (24)\end{matrix}$

[0179] up to the last m stages of the differential amplifier are allbeing limited and the rest of the differential amplifiers are in thelinear gain region. Therefore, the RSSI is shown to be:

A ²β² v _(in) ² +A ⁴β⁴ v _(in) ⁴ +. . . +A ^(2(n−m))β^(2(n−m)) v _(in)^(2(n−m)) +mβ ² S ² =RSSI  (25)

[0180] This is further simplified to: $\begin{matrix}{{RSSI} = {{\frac{\left( {A\quad \beta} \right)^{2}}{\left( {A\quad \beta} \right)^{2} - 1}{V_{in}^{2}\left\lbrack {\left( {A\quad \beta} \right)^{2{({n - m - 1})}} -} \right\rbrack}} + {m\quad \beta^{2}S^{2}}}} & (26) \\{{RSSI} \approx {{\frac{1}{\left( {A\quad \beta} \right)^{2} - 1}{V_{in}^{2}\left( {A\quad \beta} \right)}^{2{({n - m})}}} + {m\quad \beta^{2}S^{2}}}} & (27)\end{matrix}$

[0181] The above equation is a first order approximation to thelogarithmic function shown in equation (28) according to the first twoterms of the Taylor expansion at a given operating point

IdealRSSI=ClogV _(in) ²  (28)

[0182] The following calculates the constant C from the maximum andminimum of the RSSI:

MaxRSSI−MinRSSI=ClogA ^(2n)  (29)

ΔRSSI=ClogA ^(2n)  (30) $\begin{matrix}{C = \frac{\Delta \quad {RSSI}}{2n\quad \log \quad A}} & (31) \\{{({Ideal}){RSSI}} = {\frac{\Delta \quad {RSSI}}{2n\quad \log \quad A}\log \quad V_{in}^{2}}} & (32)\end{matrix}$

[0183] To find the relation between the gain of a differentialamplifier, the gain of a rectifier, and the maximum input range of thecombined differential amplifier and the rectifier, the RSSI will becalculated for the two consecutive differential amplifier and rectifiercombinations (see equations (33) and (34)) for both ideal RSSI equations(32) and approximated RSSI equation (27): $\begin{matrix}{V_{in1} = \frac{S}{(A)^{n - m}}} & (33) \\{V_{in2} = \frac{S}{(A)^{n - m - 1}}} & (34)\end{matrix}$

 (Ideal)RSSI ₂ −RSSI ₁=log(A)²  (35)

(Approximated)RSSI ₂ −RSSI ₁=β² S ²  (36)

[0184] Therefore,

Clog(A)²=β² S ⁶²  (37)

[0185] Using equations (18) and (12), the following expression isachieved: $\begin{matrix}{\frac{\Delta \quad {RSSI}}{n} = {\beta^{2}S^{2}}} & (38)\end{matrix}$

[0186] Plugging equation (19) into (8) results in the following:$\begin{matrix}\begin{matrix}{{RSSI} = {{\frac{1}{\left( {A\quad \beta} \right)^{2} - 1}\left( {A\quad \beta} \right)^{2{({n - m})}}V_{in}^{2}} +}} \\{{{m\frac{\Delta \quad {RSSI}}{n}};{\frac{S}{A^{n - m}} < V_{in} < \frac{S}{A^{n - m - 1}}}}}\end{matrix} & (39)\end{matrix}$

[0187]FIG. 16(a) shows a schematic diagram for an exemplary embodimentof the differential amplifier used in the type II core amplifier. Thedifferential input signal is fed to the gates of transistor amplifiers955, 957. The amplified differential output signal is provided at thedrains of the transistor amplifiers 955, 957. The gain of the transistoramplifiers is set by load transistors 958, 860, each connected betweenthe drain of one of the transistor amplifiers and a power source. Moreparticularly, the gain of the differential amplifier is determined bythe ratio of the square root of transistor amplifiers-to-loadtransistors. $\begin{matrix}\begin{matrix}{{{Gain}(A)} = \sqrt{\frac{w_{in}}{w_{in}}}} \\{= \sqrt{\frac{200}{6} = 5.8}}\end{matrix} & (40)\end{matrix}$

[0188] The sources of the transistor amplifiers 955, 957 are connectedin common and coupled to a constant current source transistor 952. Inthe described exemplary embodiment, the controller provides the bias tothe gate of the transistor 952 to set the current.

[0189] An exemplary embodiment of the full-wave rectifier with twounbalanced source-coupled pairs cross-coupled is shown in FIG. 16(b). Inthis embodiment, the differential input signal is fed to an unbalancedpair of transistors. One of the differential input pairs is fed to thegates of the unbalanced transistor pair 968, 966 and the otherdifferential input pair is fed to the gates of the other unbalancedtransistor pair 964, 962. The drains of transistors 968, 962 areconnected in common and provide one of the differential output pairs.The drains of transistors 964, 966 are connected in common and providethe other differential output pair. Transistors 968, 964 are connectedin a common source configuration and coupled to a constant currentsource transistor 965. Transistors 962, 966 are also connected in acommon source configuration with the common source connected to acurrent source transistor 967. The gates of the current sources 965, 967are connected together. In the described exemplary embodiment, thecontroller provides the bias to the common gate connection to set thecurrent.

[0190] Transistors 970 and 971 provide a current-mirror load tocross-coupled transistors 968, 962. Similarly, transistors 972, 973provide a current-mirror load to cross-coupled transistors 962, 964. Thecurrent through the cross-coupled transistors 962, 964 is the sum of thecurrent through the load transistor 972 and the current through the loadtransistor 971 which is mirrored from the load transistor 970. Thecurrent through the cross-coupled transistors 962, 962 is also mirroredto load transistor 973 for the RSSI output.

[0191] When the transistors 962, 964, 966, and 968 are operating in thesaturation region, the following equations are shown for thedifferential output current DI_(SQB1) where k is the ratio of the twounbalanced source-coupled transistors: $\begin{matrix}\begin{matrix}{{{if}\quad \Delta \quad I_{SQM1}} = {\left( {I_{D1} + I_{D4}} \right) - \left( {I_{D2} + I_{D3}} \right)}} \\{= {2\left( {I_{DC} + I_{SQ}} \right)}} \\{= {{2\frac{k - 1}{k + 1}I_{o}} - {4\frac{k\left( {k - 1} \right)\beta_{N}}{\left( {k + 1} \right)^{2}}V_{I}^{2}}}}\end{matrix} & (41)\end{matrix}$

[0192] The input dynamic range of the full rectifier is then:$\begin{matrix}{{{{if}\quad \Delta \quad I_{SQM1}} = O},{V_{i} = {{\pm \frac{\sqrt{I_{o}}}{\beta_{N}}}\frac{\sqrt{k + 1}}{2k}}}} & (42)\end{matrix}$

[0193] The full-wave rectifier includes two unbalanced differentialpairs with a unidirectional current output. One rectifier 976 taps eachdifferential pair and sums their currents into a 10 kW resistor R_(L).

[0194] The square law portion of equation (41) multiplied by theresistance provides the β²S² of equation (42): $\begin{matrix}{{\beta^{2}S^{2}} = {4\frac{k\left( {k - 1} \right)\beta_{N}}{\left( {k + 1} \right)^{2}}V_{i}^{2}R_{L}}} & (43)\end{matrix}$

[0195] By plugging the V_(i) from equation (42) and replacing β²S² fromequation (38), the following relation is obtained: $\begin{matrix}{\frac{\Delta \quad {RSSI}}{n} = {2\frac{k - 1}{k + 1}I_{o}R_{L}}} & (44)\end{matrix}$

[0196] For ΔRSSI=1V, n=7 stages, R_(L)=10000Ω, and k=4, from the aboveequation I₀ is calculated to be 12 mA. Therefore, each rectifier will bebiased with two 12 mA current sources (one 12 ma current source for theI signal and a second 12 ma current source for the Q channel). Thisresults in an approximately logarithmic voltage, which indicates thereceived signal-strength (RSSI).

[0197] 1.4 Complex IF Mixers

[0198] The IF down conversion to baseband signal can be implementedusing four fully balanced quadrature mixers as shown in FIG. 17(a). Thismixer configuration includes both quadrature inputs from theprogrammable multiple stage amplifier and quadrature IF clocks from theLO generator. This configuration produces single sideband, quadraturebaseband signals, with minimum number of spurs at the output. Thesecharacteristics aid in relaxing the baseband filtering as well assimplifying the demodulator architecture. An IF mixer buffer 352 buffersthe IF clock (Clk_I, Clk_Q as shown in FIG. 17(a)).

[0199] The outputs of the limiters are coupled to the quadrature clocksof the IF mixers (I_in for mixer 322, I_in for mixer 323, Q_in for mixer324, Q_in for mixer 325) and the IF clocks are coupled to the data inputof the IF mixers. This configuration minimizes spurs at the output ofthe IF mixers because the signal being mixed is the IF clocks which is aclean sine wave, and therefore, has minimal harmonics. The limitingaction of the programmable multiple stage amplifier on the I and Q datawill have essentially no effect on the spurs at the output of the IFmixers. FIG. 17b shows the IF mixer clock signal spectrum which containsonly odd harmonics. The IF signals do not have even harmonics inembodiments of the present invention using a fully differentialconfiguration. The bandwidth of the m′th(=2n+1) harmonic is directlyproportional to mfs, whereas its amplitude is inversely proportional tomfs. FIG. 17c shows the sinusoidal input spectrum of the IF clocks. FIG.17d shows the IF mixer output spectrum.

[0200] 1.5 Clock Generator

[0201] A clock generator can be used to generate a quadrature sinusoidalsignal with controlled amplitude. The clock generator can be located inthe receiver, or alternatively the LO Generator, and provides a cleansinusoidal IF from the square wave output of the divider in the LOGenerator for downconverting the IF signal in the receiver path tobaseband. FIG. 18 shows a block diagram and signal spectrum of a clockgenerator. A sinusoidal signal is generated from a square-wave usingcascaded polyphase. FIG. 18 shows a clock generator block diagram. Theclock generator outputs clk_I and clk_Q for the IF mixer buffer (seeFIG. 17). The clock generator includes a polyphase filter at 3 fs 360, apolyphase filter at 5 fs 362, and a low pass filter 364. FIG. 19a showsthe input clock signal spectrum. FIG. 19b shows the spectrum at 3 fs 366and at 5 fs 368 polyphase. FIG. 19c shows the sinusoidal signalgeneration after the low pass filter 364.

[0202] In fully integrated embodiments of the present invention, thecontroller can provide self calibration to generate precise signallevels with negligible dependency on the process variations. The twopolyphase filters 360, 362 with RC calibration can be used to remove thefirst two odd harmonics of the signal. The remaining harmonics can befiltered with an on chip tunable low pass filter. The output of theclock generator block is a quadrature sinusoidal signal with controlledsignal level. This spectrally clean signal is used at the input ofcomplex IF mixers to downconvert the IF signal to baseband.

[0203] 1.6 Programmable Low Pass Filter

[0204] The first major spurs out of downconversion process is at 4 timesthe IF frequency. A self calibrated 4 fs polyphase filter can be usedafter the complex IF mixers to reduce the spurious and improve thelinearity of the demodulator.

[0205] The polyphase filter can be implemented with two back to backpolyphase to reject both positive phase and the negative phase. Built-inprogrammability can also be included for operating with otherfrequencies. This capability enables the demodulator to be highlyflexible. It can support wide range of incoming IF frequencies and withdifferent modulation schemes.

[0206] Following the polyphase filter, a quadrature lowpass filter canbe used to remove unwanted spurs. The lowpass filter can be programmableand designed to minimize group delay distortion without sacrificing highfrequency filtering characteristics.

[0207] In fully integrated embodiments of the present invention, thecontroller can provide on chip RC calibration to minimize any processvariation. The programmability of the polyphase filter and the low passfilter adds a new degree of flexibility to the system; it can be used toaccommodate different data bandwidths.

[0208]FIG. 20 shows a baseband spectrum filtering before thediscriminator. FIG. 20(a) shows the signal spectrum at polyphase input,i.e., the frequency spectrum of the polyphase filter. FIG. 20(b) showsthe signal spectrum at polyphase output, i.e. the frequency spectrum ofthe low pass filter. FIG. 20(c) shows the signal spectrum at the lowpass filter output.

[0209] 1.7 High Data Rate Frequency Demodulator

[0210] The demodulator may take on various forms to accommodatedifferent modulation schemes. One embodiment of the demodulation used inconnection with the present invention includes a low power, monolithicdemodulator for high data rates in frequency modulated systems. Thisdemodulator can provide data recovery for well over 1-MHz data rates.

[0211] The demodulator can be FSK or GMSK demodulator. FSK is digitalfrequency modulation. GMSK is a specific type of FSK. GMSK stands forGaussian filtered FSK modulation, which means that GMSK has gaussianfiltering at the output of frequency modulation. GMSK has more stringentrequirements than FSK. The data rate is higher for GMSK and themodulation index is low for GMSK relative to FSK.

[0212] The described embodiment of the demodulator is a low power, fullyintegrated FSK/GMSK demodulator for high data rates and low modulationindex. The FSK operates with the programmable gain stage amplifier as alimiter, and therefore, does not require oversampling clocks or complexAGC blocks.

[0213]FIG. 21 is a block diagram of an exemplary high data ratefrequency demodulator in accordance with the present invention. Thedemodulator performs a balanced quadrature demodulation. Differentiators329, 330 convert the baseband signal to a signal having an amplitudeproportional to the baseband signal frequency. One differentiator 329converts the I signal and the other differentiator 330 converts the Qsignal. The I signal output of the differentiator 329 is coupled to amultiplier 331 where it is multiplied by the Q signal input into thedemodulator. The Q signal output of the differentiator 330 is coupled toa multiplier 332 where it is multiplied by the I signal input into thedemodulator. The multipliers 331, 332 produce a single ended DC signal.The DC signals are summed together by summation circuit 333. A peakdetector/slicer 334 digitizes the DC signal from the summation circuit,thereby producing discrete zeros and ones.

[0214] The frequency discrimination can be performed using adifferentiator as shown in FIG. 22. A differential input signal iscoupled to the input of an amplifier 340 through capacitors 341, 342. Afeedback resistor 343, 344 is coupled between each differential output.Its operation is based on generating an output signal level linearlyproportional to the incoming signal frequency. In other words, thehigher the incoming frequency, the larger signal amplitude output by thedifferentiator. Therefore, it is desirable to have a spur free signal atthe input of this stage. High frequency spurs can degrade theperformance of the differentiator. By using the polyphase filter inconjunction with the lowpass filter (see FIG. 2) before the demodulator,a nearly ideal baseband signal is input to the differentiator. Thecapacitors 341, 342 in the signal path with the resistive feedbackoperation of the amplifier is proportional to the time derivative of theinput. For a sinusoidal input, V(in)=A.sin(ωt), the output will beV(out): d/dt(V(in))=to.A.cos(ωt). Thus, the magnitude of the outputincreases linearly with increasing frequency.

[0215] The controller provides RC calibration to keep thedifferentiation gain process invariant. In order to reduce the effect ofany high frequency coupling to the differentiator input, thedifferentiator gain is flattened out for frequencies beyond the band ofinterest. In addition to frequency discrimination, the differentiationprocess adds a 90 degrees phase shift to the incoming signal. This phaseshift is inherent to differentiation process. Since the output is inquadrature phase with the input (except for differing amplitude), crossmultiplication of the input and output results in frequency information.

[0216]FIG. 23 shows an exemplary analog multiplier 331, 332 with zerohigher harmonics in accordance with the present invention. Buffers one334 and two 335 are added to a Gilbert cell to linearize the voltagelevels. Buffers one 334 and two 335 convert the two inputs into twovoltage levels for true analog multiplication using a Gilbert cell. TheGilbert cell is comprised of transistors 336, 338, resistors 340, 342and cross-coupled pairs of transistors 344, 346 and transistors 348,350.

[0217] By cross multiplying the input and the output signals to thedifferentiator, the amplitude information is generated. Since thesignals are at baseband, it can be difficult to filter out any spursresulting from the multiplication process. Linearized buffers can beused to minimize spurs by providing a near ideal analog multiplier. Onchip calibration can also be used to control the multiplication gain andto minimize process variation dependency. In order to accommodate highdata rates such as 1 MHz and beyond, all the stages should have lowphase delays. In addition, matching all the delays in quadrature signalscan be advantageous.

[0218] The output of the multiplier is a single ended DC signal which isa linear function of the frequency. This analog output can representmultilevel FSK with arbitrary modulation index. The minimum modulationindex is only limited by wireless communication fundamentals.

[0219] An exemplary peak detector/slicer for frequency data detection isshown in FIG. 24. The differential input signal is coupled to a peakdetector 346 which detects the high peak. The differential input signalis also coupled to a second peak 347 detector which detects the lowvalley of the signal. The outputs of the peak detectors are coupled to aresistor divider network 348, 349 to obtain the average of the outputsignal. The average signal output from the resistor divider network isused as the calibrated zero frequency to obviate frequency offsetproblems due to the frequency translation process from IF to baseband.

[0220] A differential amplifier 345 is used to digitize the frequencyinformation by comparing the differential input signal with thecalibrated zero frequency. The output of the amplifier is a logic “1” ifthe baseband frequency is greater than the calibrated zero frequency anda logic “0” if the baseband frequency is less than the calibrated zerofrequency. The output is amplified through several inverters 350 whichin turn generate digital rail to rail output.

[0221] 2.0. Transmitter

[0222] 2.1 Differential Power Amplifier

[0223] In an exemplary embodiment of the invention, the PA is adifferential PA as shown in FIG. 25. The symmetry of the differential PAin conjunction with other features supports implementation in a varietyof technologies including CMOS. The described embodiment of thedifferential PA can be a fully integrated class A PA. A balun 610 isused to connect the PA to an antenna or a duplexer. The balun convertsthe differential signal to a single-ended output.

[0224] The described embodiments of the differential PA is a two stagedevice. The two stages minimize backward leakage of the output signal tothe input stage. As those skilled in the art will appreciate, any numberof stages can be implemented depending on the particular application andoperating environment Equal distribution of gain between the two stageshelps prevents oscillation by avoiding excess accumulation of gain inone stage. A cascode architecture may be incorporated into the PA toprovide good stability and insulation.

[0225] The input stage or pre-amplifier of the power amplifier includesan input differential pair comprising amplifying transistors 612, 614.Transistor 616 is a current source that biases the input differentialpair. The presence of a current source provides many positive aspectsincluding common mode rejection. The current is controlled by thevoltage applied to the gate of transistor 616. The gate voltage shouldbe chosen to prevent the transistor 616 from operating in the trioderegion. Triode operation of transistor 616 has a number of drawbacks.Primarily, since transistor 616 is supposed to act as a current source,its operation in the triode region can cause distortion in the currentflowing into the transistor 612 and the transistor 614, and consequentlygives rise to nonlinearity in the signal. Secondly, the triode behaviorof transistor 616 will depend on temperature and process variations.Therefore, the circuit operation will vary over different process andtemperature corners.

[0226] Cascode transistors 618, 620 provide stability by isolating theoutput from the input. As a result, no change in the input impedanceoccurs over frequency. The gates of the cascode transistors 618, 620devices are biased through a bond wire. A resistor 622 in series withthe gates of the cascode transistors prevents the inductance associatedwith the bonding from resonating with the input capacitive of thetransistors, thereby improving stability. The resistor 622 incombination with the gates of transistors 618, 620 also improves commonmode rejection and makes the transistor input act like a virtual groundat RF. Resistor 623 isolates the power supply from the PA and providescommon mode rejection by increasing the symmetry of the differential PA.Inductors 624, 626 tune out the capacitance at the drains of thetransistors 618, 620. At the tuning frequency, the impedance seen at thedrains of the transistors 618, 620 is high, which provides the high gainat the tuning frequency.

[0227] The differential output of the input stage is provided at thedrains of the cascode transistors 618, 620 to AC coupling capacitors628, 630. Capacitor 628 couples the drain of transistor 618 with thegate of transistor 632. Capacitor 630 couples the drain of transistor620 with the gate of transistor 634. The transistors 632, 634 provideamplification for the second stage of the PA. Resistors 636, 638 arebiasing resistors for biasing the transistors 632, 634.

[0228] In the output stage of the PA, the current level is higher andthe size of the current source should be increased to maintain the samebias situation. However, large tail devices can lower the common moderejection. Accordingly, instead of a current source, an inductor 640 canbe used to improve the headroom. The inductor 640 is a good substitutefor a current source. The inductor 640 is almost a short circuit at lowfrequencies and provides up to 1 Kohm of impedance at RF. By way ofexample, a 15 nH inductor with proper shielding (to increase the Q) anda self-resonance frequency close to 4.5 GHz can be used for optimum highfrequency impedance and sufficient self-resonance.

[0229] Inductors 622, 624 tune out the capacitance at the drains oftransistors 632, 634. Capacitors 642, 644 are AC coupling capacitors.Inductors 646 and capacitor 648 match the output impedance of the PA tothe antenna, by way of example, 50 Ω. Similarly, inductors 650 andcapacitor 652 match the output impedance of the PA to the antenna. Balun610 is a differential to single-ended voltage converter. Resistance 654is representative of the load resistance.

[0230] Capacitances associated with bias resistors may also beaddressed. Consider a typical distributed model for a polysilicon(“poly” for short) resistor. Around 4 fF to substrate can be associatedwith every kilo-ohm of resistance in a poly resistor. This means that,for example in a 20 Kohm resistor, around 80 fF of distributedcapacitance to the substrate exists. This can contribute to power lossbecause part of the power will be drained into the substrate. One way ofbiasing the input stage and the output stage is through a resistivevoltage divider as shown in FIG. 26(a). The biasing of the input stageis shown for the transistor 616 in FIG. 25, however, those skilled inthe art will readily appreciate that the same biasing circuit can beused for the transistor 614 (FIG. 25). One drawback from this approach,however, is that the gate of the transistor will see the capacitancefrom the two resistors 658, 660 of the voltage divider. Capacitor 662 isa coupling capacitor, which couples the previous stage to the voltagedivider. Switch 664 is for powering down the stage of the poweramplifier that is connected to the voltage divider. The switch 664 is onin normal operation and is off in power down mode.

[0231]FIG. 26(b) is similar to FIG. 26(a), except that FIG. 26(b)includes resistor 666. DC-wise the FIG. 26(a) and FIG. 26(b) circuitsare the same. However, in AC, not only is the resistance seen from thegates of transistors 634, 632 towards the resistive bias network bigger,but the capacitance is smaller because the capacitance is caused byresistor 666 and not resistors 660, 658. Since there is lesscapacitance, there is less loss of the signal. From FIG. 25, transistors618, 620 in the input stage and transistors 632, 634 in the output stagecan be biased by the resistive voltage divider shown in FIG. 26(b).

[0232]FIG. 27 shows an exemplary bias circuit for the current sourcetransistor 616 of FIG. 25. To fix the bias current of the circuit overtemperature and process variation, a diode-connected switch transistor672 may be used with a well-regulated current 670. The voltage generatedacross the diode-connected transistor 672 is applied to the gate of thecurrent source transistor 616. Because of the mirroring effect of thisconnection and since all transistors move in the same direction overtemperature and process corners, the mirrored current will be almostconstant. The reference current is obtained by calibration of a resistorby the controller. The calibrated resistor can be isolated from the restof the PA to prevent high frequency coupling through the resistor toother transceiver circuits. As those skilled in the art will appreciate,the exemplary bias circuit is not limited to the current sourcetransistor of the PA and may be applied to other transistors requiringaccurate biasing currents.

[0233]FIG. 28 shows an exemplary power control circuit. The powercontrol circuit can provide current scaling. The power control circuitchanges power digitally by controlling the bias of the current sourcetransistor 616 of the first differential pair 612, 614 in the PA (FIG.25). The power control circuit can be used in any application requiringdifferent power levels. The power control is done by applying differentvoltage levels to the gate of the current source in the first stage(input stage or preamplifier) of the PA. A combination of currentadjustment in both stages (input stage and output stage) of the PA canalso be done. Different voltage levels are generated corresponding todifferent power levels. In one embodiment of the invention, the powercontrol circuit has four stages as shown in FIG. 28. Alternatively, thepower control circuit can have any number of stages corresponding to thenumber of power levels needed in an application.

[0234] The power control circuit includes transistor pairs in parallel.Transistors 674, 676, 678, 680 are switch transistors and are coupled todiode-connected transistors 682, 684, 686, 688, respectively. The switchtransistors 674, 676, 678, 680 are coupled to a current source 670. Eachdiode-connected transistor 682, 684, 686, 688 can be switched into theparallel combination of by turning its respective switching transistoron. Conversely, any diode-connected transistor can be removed from theparallel combination by turning its respective switch transistor off.The current from the current source 670 is injected into a parallelcombination of switch transistors 674, 676, 678, 680. The power levelcan be incremented or decremented by switching one or more switchtransistors into the parallel combination. By way of example, a decreasein the power level can be realized by switching a switch transistor intothe parallel combination. This is equivalent to less voltage drop acrossthe parallel combination, which in turn corresponds to a lower powerlevel. A variety of stages are comprehended in alternative embodimentsof the invention depending on the number of power levels needed for agiven application. A thermometer code from the controller can be appliedto the power control circuit according to which the power level isadjusted.

[0235] As described above, the output of the PA can be independentlymatched to a 500 ohm load. The matching circuit (inductors 646, 650 andcapacitors 648, 652) is connected to the balun. Any non-ideality of thebalun, bond wire impedance, pin/PCB capacitance, and other parasiticscan be absorbed by the matching circuits. High-Q inductors can be usedwhere possible. The loss in efficiency may also be tolerable with lowpower applications.

[0236] 2.2 Single-Ended Differential Power Amplifier

[0237] In another embodiment of the present invention, the balun can beeliminated by a single-ended to differential PA. FIG. 29 shows theoutput stage of a single-ended to differential PA. The output stageincludes resistors 690, 692, inductors 694, 696, 698, and transistors700, 702. Coupling capacitor 704 couples the output stage to an LCcircuit, the LC circuit including inductor 706 and capacitor 708.Coupling capacitor 710 couples the second stage to a CL circuit, the CLcircuit comprising capacitor 712 and inductor 714. The transistors 700,702 provide amplification of the differential signal applied to theoutput stage of the PA. The output of the amplifying transistors 700,702 produces two signals 180 degrees out of phase. The LC circuit isused to match the first output to a 100 ohm load 718 and to shift thephase of the signal by 90 degrees. The CL circuit is deployed to matchthe second output to a 100 ohm load 720, and to shift the phase of thesignal in the opposite direction by 90 degrees. Since the two outputswere out of phase by 180 degrees at the beginning and each underwent anadditional 90 degrees of shift (in opposite directions) the two signalsappearing across the two 100 ohm loads will be in phase. In an idealsituation, they will also be of similar amplitudes. This means that thetwo nodes can be connected together to realize a single-ended signalmatched for a 50 ohm load 716.

[0238] Unlike the differential PA, the differential to single-endedconfiguration does not enjoy the symmetry of a fully differential path.Accordingly, with respect to embodiments of the present inventionintegrated into a single IC, the effect of bond wires should beconsidered. Because of stability and matching issues, a separate ground(bond wire) for the matching circuit should be used. The bond wiresshould be small and the matching should be tweaked to cancel theireffect.

[0239] The bias current to the amplifying transistors 700, 702 forembodiments of the present invention integrated into a single IC can beset in a number of ways, including by way of example, the bias circuitshown in FIG. 27. The voltage generated across the diode-connectedtransistor 672 is applied to the gate of the amplifying transistor 700.A similar bias circuit can be used for biasing the amplifying transistor702.

[0240] Alternatively, the bias circuit of the amplifying transistors700, 702 for single IC embodiments can be set with a power controlcircuit as shown in FIG. 28. The current source is connected directlythe amplifying transistor 700. By incrementally switching thediode-connected transistors 682, 684, 686, 688 into the parallelcombination, the voltage applied to the gate of the amplifyingtransistor 700 is incrementally pulled down toward ground. Conversely,by incrementally switching the diode-connected transistors 682, 684,686, 688 out of the parallel combination, the voltage applied to thegate of the amplifying transistor 700 is incrementally pulled up towardthe source voltage (not shown). A similar power control circuit can beused with the amplifying transistor 702.

[0241] 2.3. Digitally Programmable CMOS PA with On-Chip Matching

[0242] In another embodiment of the present invention, a PA isintegrated into a single IC with digitally programmable circuitry andon-chip matching to an external antenna, antenna switch, or similardevice. FIG. 30 shows an exemplary PA with digital power control. Thiscircuit comprises two stages. The input stage provides initialamplification and acts as a buffer to isolate the output stage from theVCO. The output stage is comprised of a switchable differential pair tosteer the current towards the load. The output stage also provides thenecessary drive for the antenna. The power level of the output stage canbe set by individually turning on and off current sources connected toeach differential pair.

[0243] Transistors 722, 724 provide initial amplification. Transistor726 is the current source that biases the transistors 722, 724.Inductors 728, 730 tune out the capacitance at the drains of thetransistors 722, 724. At the tuning frequency, the impedance seen at thedrains is high, which provides high gain at the tuning frequency.

[0244] Capacitors 732, 736 are AC coupling capacitors. Capacitor 732couples the drain of transistor 724 with the gate of transistor 734.Capacitor 736 couples the drain of transistor 722 with the gate oftransistor 738. Resistors 740, 742 are biasing resistors for biasing thegates of the transistors 734, 738. Transistors 734, 738 are amplifyingtransistors in the output stage of the PA. Transistor pairs 744, 746,transistor pairs 748, 750, and transistor pairs 752, 754 each provideadditional gain for the signal. Each pair can be switched in or outdepending on whether a high or low gain is needed. For maximum gain eachtransistor pair in the output stage of the PA will be switched on. Thegain can be incrementally decreased by switching out individualtransistor pairs. The PA may have more or less transistor pairsdepending on the maximum gain and resolution of incremental changes inthe gain that is desired.

[0245] Transistor 756 has two purposes. First, it is a current sourcethat biases transistors 734, 738. Second, it provides a means forswitching transistors 734, 738 in and out of the circuit to alter thegain of the output stage amplifier. Each transistors 758, 760, 762serves the same purpose for its respective transistor pair. A digitalcontrol, word from the controller can be applied to the gates of thetransistors 756, 758, 760, 762 to digitally set the power level. Thisapproach provides the flexibility to apply ramp up and ramp down periodsto the PA, in addition to the possibility of digitally controlling thepower level. The drains of the transistors 756, 758, 760, 762 areconnected to a circuit that serves a twofold purpose: 1) it converts thedifferential output to single ended output, and 2) it matches the stageto external 50 ohm antenna to provide maximum transferable gain.

[0246] Inductors 764, 766 tune out the capacitance at the drains oftransistors 752, 754. Capacitor 768 couples the PA to the load 770.Inductor 772 is a matching and phase-shift element, which advances thephase of the signal by 90°. Capacitor 794 is a matching and phase-shiftelement, which retards the phase of the signal by 90°. Capacitor 796 isthe pad capacitance. The bonding wire 798 bonds the PA to the loadresistance 770 (e.g., the antenna).

[0247] 3.0 Local Oscillator

[0248] In embodiments of the present invention utilizing a low-IF ordirect conversion architecture, techniques are implemented to deal withthe potential disturbance of the local oscillator by the PA. Since theLO generator has a frequency which coincides with the RF signal at thetransmitter output, the large modulated signal at the PA output may pullthe VCO frequency. The potential for this disturbance can be reduced bysetting the VCO frequency far from the PA output frequency. To this end,an exemplary embodiment of the LO generator produces RF clocks whosefrequency is close to the PA output frequency, as required in a low-IFor direct-conversion architectures, with a VCO operating at a frequencyfar from that of the RF clocks. One way of doing so is to use two VCO864, 866, with frequencies of f₁ and f₂ respectively, and mix 868 theiroutput to generate a clock at a higher frequency of f₁+f₂ as shown inFIG. 31(a). With this approach, the VCO frequency will be away from thePA output frequency with an offset equal to f₁ (or f₂). A bandpassfilter 876 after the mixer can be used to reject the undesired signal atf₁-f₂. The maximum offset can be achieved when f, is close to f₂.

[0249] An alternative embodiment for generating RF clocks far away infrequency from the VCO is to generate f₂ by dividing the VCO output by Nas shown in FIG. 31(1 b). The output of the VCO 864 (at f₁) is coupledto a divider 872. The output of te divider 872 (at f₂) is mixed with theVCO at mixer 868 to produce an RF clock frequency equal to:f_(LO)=f₁′(1+1/N), where f₁ is the VCO frequency. A bandpass filter 874at the mixer output can be used to reject the lower sideband located atf₁−f₁/N.

[0250] In another embodiment of the present invention, a single sidebandmixing scheme is used for the LO generator. FIG. 32 shows a singlesideband mixing scheme. This approach generates I and Q signals at theVCO 864 output The output of the VCO 864 is coupled to a quadraturefrequency divider 876 should be able to deliver quadrature outputs.Quadrature outputs will be realized if the divide ratio (N) is equal totwo to the power of an integer (N=2n). The I signal output of thedivider 876 is mixed with the I signal output of the VCO 864 by a mixer878. Similarly, the Q signal output of the divider 876 is mixed with theQ signal output of the VCO 864 by a mixer 880.

[0251] Although a single sideband structure uses two mixers, this shouldnot double the mixer power consumption, since the gain of the singlesideband mixer will be twice as much. By utilizing a Gilbert cell (i.e.,a current commutating mixer) for each mixer 878, 880, the addition orsubtraction required in a single sideband mixer can be done byconnecting the two mixers 878, 880 outputs and sharing a common load(e.g., an LC circuit). The current from the mixers is added orsubtracted, depending on the polarity of the inputs, and then convertedto a voltage by an LC load (not shown) resonating at the desiredfrequency.

[0252]FIG. 33 shows an LO generator architecture in accordance with anembodiment of the present invention. This architecture is similar to thearchitecture shown in FIG. 32, except that the LO generator architecturein FIG. 33 generates I-Q data. In a low-IF system, a quadrature LO isdesirable for image rejection. In the described embodiment, the I and Qoutputs of the VCO can be applied to a pair of single sideband mixer togenerate quadrature LO signals. A quadrature VCO 48 produces I and Qsignals at its output. Buffers are included to provide isolation betweenthe VCO output and the LO generator output. The buffer 884 buffers the Ioutput of the VCO 48. The buffer 886 buffers the Q output of the VCO 48.The buffer 888 combines the I and Q outputs of the buffers 884, 886. Thesignal from the buffer 888 is coupled to a frequency divider 890 whereit is divided by N and separated into I and Q signals. The I-Q outputsof the divider 890 are buffered by buffer 892 and buffer 894. The Ioutput of the divider 890 is coupled to a buffer 892 and the Q signaloutput of the divider 890 is coupled to a buffer 894. A first mixer 896mixes the I signal output of the buffer 892 with the I signal output ofthe buffer 884. A second mixer 897 mixes the Q signal output from thebuffer 894 with Q signal output from the buffer 886. A third mixer 898mixes the Q signal output of the buffer 894 with the I signal output ofthe buffer 884. A fourth mixer 899 mixes the I signal output from thebuffer 892 with the Q signal output from the buffer 886. The outputs ofthe first and second mixers 896, 897 are combined and coupled to buffer900. The outputs of the third and fourth mixers 898, 899 are combinedand coupled to buffer 902. LC circuits (not shown) can be positioned atthe output of each buffer 900, 902 to provide a second-order filterwhich rejects the spurs and harmonics produced due to the mixing actionin the LO generator.

[0253] Embodiments of the present invention which are integrated into asingle IC may employ buffers configured as differential pairs with acurrent source to set the bias. With this configuration, if theamplitude of the buffer input is large enough, the signal amplitude atthe output will be rather independent of the process parameters. Thisreduces the sensitivity of the design to temperature or processvariation.

[0254] The lower sideband signal is ideally rejected with the describedembodiment of the LO generator because of the quadrature mixing.However, in practice, because of the phase and amplitude inaccuracy atthe VCO and divider outputs, a finite rejection is obtained. In singleIC fully integrated embodiments of the present invention, the rejectionis mainly limited to the matching between the devices on chip, and istypically about 30-40 dB. Since the lower sideband signal is 2×f₁/N awayin frequency from the desired signal, by proper choice of N, it can befurther attenuated with on-chip filtering.

[0255] Because of the hard switching action of the buffers, the mixerswill effectively be switched by a square-wave signal. Thus, the divideroutput will be upconverted by the main harmonic of VCO (f₁), as well asits odd harmonics (n×f₁), with a conversion gain of 1/n. In addition, atthe input of the mixer, because of the nonlinearity of the mixers, andthe buffers preceding the mixers, all the odd harmonics of the inputsignals to the mixers will exist. Even harmonics, both at the LO and theinput of the mixers can be neglected if a fully balanced configurationis used. Therefore, all the harmonics of VCO (n×f₁) will mix with allthe harmonics of input (m×f₂), where f₂ is equal to f₁/N. Because of thequadrature mixing, at each upconversion only one sideband appears at themixer output Upper or lower sideband rejection depends on the phase ofthe input and LO at each harmonic. For instance, for the main harmonicsmixed with each other, the lower sideband is rejected, whereas when themain harmonic of the VCO mixes with the third harmonic of the divideroutput signal, the upper sideband is rejected. Table 1 gives a summaryof the cross-modulation products up to the 5′ harmonic of the VCO andinput. In each product, only one sideband is considered, since the otherone is attenuated due to quadrature mixing, and is negligible.

[0256] All the spurs are at least 2×f₁/N away from the main signallocated at f₁×(1+1/N). The VCO frequency will be f₁/N away from the PAoutput. Thus, by choosing a smaller N better filtering can be obtained.In addition, the VCO frequency will be further away from the PA outputfrequency. The value of N, and the quality factor (Q) of the resonators(not shown) positioned at the output of each component determine howmuch each spur will be attenuated. The resonator quality factor isusually set by the inductor Q, and that depends merely on the ICtechnology. Higher Q provides better filtering and lower powerconsumption. TABLE 1 Cross-Modulation Products at the LO GeneratorOutput 1^(st): f₁/N 3^(rd): 3f₁/N 5^(th): 5f₁/N 1^(st): f₁ f₁ × (1 +1/N) f₁ × (1 − 3/N) f₁ × (1 + 5/N) 3^(rd): 3f₁ f₁ × (3 − 1/N) f₁ × (3 +3/N) f₁ × (3 − 5/N) 5^(th): 5f₁ f₁ × (5 + 1/N) f₁ × (5 − 3/N) f₁ × (5 +5/N)

[0257] The maximum filtering is obtained by choosing N=1. Moreover, inthis case, the frequency divider is eliminated. This lowers the powerconsumption and reduces the system complexity of the LO generator.However, the choice of N=1 may not be practical for certain embodimentsof the present invention employing a low-IF receiver architecture withquadrature LO signals. The problem arises from the fact that the thirdharmonic of the VCO (at 3 f₁) mixed with the divider output (at f₁) alsoproduces a signal at 2 f, which has the same frequency as the maincomponent of the RF clock output from the LO generator. With theconfiguration shown in FIG. 33, the following relations hold for themain harmonics:

Cos(ω₁ t)·Cos(ω₁ t)−Sin(ω₁ t)·Sin(ω₁ t)→Cos(2ω₁ t)  (45)

[0258] and

Cos(ω₁ t)·Sin(ω₁ t)+Sin(ω₁ t)·Cos(ω₁ t)→Sin(2ω₁ t)  (46)

[0259] which show that at the output of the mixers, quadrature signalsat twice the VCO frequency exist. For the VCO third harmonic mixed withthe divider output, however, the following relations hold:

−Cos(ω₁ t)·⅓Cos(3ω₁ t)−Sin(ω₁ t)·⅓Sin(3ω₁ t)→−⅓Cos(2ω₁ t)  (47)

[0260] and

Cos(ω₁ t)·⅓Sin(3ω₁ t)−Sin(ω₁ t)·⅓Cos(3ω₁ t)→−⅓Sin(2ω₁ t)  (48)

[0261] The factor ⅓ appears in the above equations because the thirdharmonic of a square-wave has an amplitude which is one third of themain harmonic. Comparing equation (46) with equation (48), the twoproducts are added in equation (46), while they are subtracted inequation (47). The reason is that for the main harmonic of the VCO,quadrature outputs have phases of 0 and 90°, whereas for the thirdharmonic, the phases are 0 and 270°. The same holds true for equation(45) and equation (47). The two cosines in equation (45) and equation(47), when added, give a cosine at 2ω₁ with an amplitude of ⅔, yet thetwo sinewaves in equation (46) and equation (48) when added, give acomponent at 2ω₁ with an amplitude of {fraction (4/3)}. Therefore, asignificant amplitude imbalance exists at the I and Q outputs of themixers. When these signals pass through the nonlinear buffer at themixers output, the amplitude imbalance will be reduced. However, becauseof the AM to PM conversion, some phase inaccuracy will be introduced.The accuracy can be improved with a quadrature generator, such as apolyphase filter, after the mixers. A polyphase filter, however, islossy, especially at high frequency, and it can load its previous stageconsiderably. This increases the LO generator power consumptionsignificantly, and renders the choice of N=1 unattractive forembodiments of the present invention employing a low-IF receiverarchitecture with quadrature LO signals.

[0262] For N=2, the LO generator output will have a frequency of 1.5 f₁,and the closest spurs will be located ±f₁ away from the output. Thesespurs can be rejected by positioning LC filters (not shown) at theoutput of each circuit in the LO generator. A second-order LC filtertuned to f₀, with a quality factor Q, rejects a signal at a frequency off as given in the following equation: $\begin{matrix}{{{H(f)}} = \frac{\frac{f}{{Qf}_{0}}}{\sqrt{\left\lbrack {1 - \left( \frac{f}{f_{0}} \right)^{2}} \right\rbrack^{2} + \left( \frac{f}{{Qf}_{0}} \right)^{2}}}} & (49)\end{matrix}$

[0263] The following discussion changes based on the Q value.Considering a Q of about 5 for the inductor, with f₀=1.5 f₁, the spurlocated at 2.5 f₁ is rejected by about 15 dB by each LC circuit. Thisspur is produced at the LO generator output due to the mixing of the VCOthird harmonic (at 3 f₁) with the divider output (at 0.5 f₁). Thissignal is attenuated by 10 dB since the third harmonic of a square-waveis one third of the main harmonic, 15 dB at the LC resonator at themixers output tuned to 1.5 f₁, and another 15 dB at the output of thebuffers (900, 902 in FIG. 33). This gives a total rejection of 40 dB.When applied to the mixers in the transmitter, this LO generator outputwill upconvert the baseband data to 2.5 f₁. With LC filters (not shown)positioned at the upconversion mixers and PA output in the transmitter,another 15+15=30 dB rejection is obtained (FIG. 33).

[0264] The spur located at 0.5 f₁ is produced because of the thirdharmonic of the divider output (at 1.5 f₁) is mixed with the VCO output(at f₁). Because of the hard switching action at the divider output, thethird harmonic is about 10 dB lower than the main harmonic at 0.5 f₁.The buffer at the divider output tuned to 0.5 f₁ (892, 8943 in FIG. 33),rejects this signal by about 22 dB (equation (24)). This spur can befurther attenuated by LC circuits at the mixer and its buffer output by(2)(22)=44 dB. The total rejection is 76 dB.

[0265]FIG. 33(a) shows a signal passing through a limiting buffer 910(such as the buffers implemented in the LO generator). When a largesignal at a frequency of f accompanied with a small interferer at afrequency of Δf 902 away pass through a limiting buffer, at the limiteroutput the interferer produces two tones ±Δf 914, 916 away from the mainsignal, each with 6 dB lower amplitude. Therefore, the spur at 2.5 f₁will actually be 10+15+15+6=46 dB attenuated when it passes through thebuffer, instead of the 40 dB calculated above. It will also produce animage at 0.5 f₁ which is 10+15+22+6=53 dB lower than the main signal.This will dominate the spur at 0.5 f₁ because of the third harmonic ofthe divider mixed with the VCO signal, which is more than 75 dB lowerthan the main signal.

[0266] Since the buffer is nonlinear, another major spur at the LOgenerator output is the third harmonic of the main signal located at3×1.5 f₁. This signal will be 10+22=32 dB lower than the main harmonic.The 22 dB rejection results from an LC circuit (not shown) tuned to 1155f₁ (equation (49)) in the buffer. This undesired signal will not degradethe LO generator performance, since even if a perfect sinewave isapplied to upconversion (or downconversion) mixers, due to hardswitching action of the buffer, the mixer is actually switched by asquare-wave whose third harmonic is only 10 dB lower. Thus, if anonlinear PA is used in the transmitter, even with a perfect input tothe PA, the third harmonic at the transmitter output will be 10+22+10=42dB lower. The first 10 dB is because the third harmonic of a square-waveis one third of the main one, the 22 dB is due to the LC filter at thePA output, and the last 10 dB is because the data is spread in thefrequency domain by three times. Any DC offset at the mixer input in thetransmitter is upconverted by the LO, and produces a spur at f₁. Thisspur can be attenuated by 13 dB for each LC circuit used (equation(49)). In addition, the signal at the mixer input in the transmitter isconsiderably larger (about 10-20 times) than the DC offset. Thus thespur at f₁ will be about 13+13+26=52 dB lower than the main signal. Allother spurs given in Table 1 are more than 55 dB lower at the LOgenerator output. The dominant spur is the one at 2.5 f₁ which is about46 dB lower than the main signal.

[0267] Choosing N>2 may not provide much benefit for single ICembodiments of the present invention with the possible exception thatthe on-chip filtering requirements may be relaxed. When using an oddnumber for N, further disadvantages may be realized because the divideroutput will not be in quadrature thereby preventing single sidebandmixing. In addition, for N>2 the divider becomes more complex and thepower consumption increases. Nevertheless, in certain applications, N=4may be selected over N=2 so that the divider quadrature accuracy willnot depend on the duty cycle of the input signal.

[0268] When choosing N equal to 2, such as N=2, quadrature signals arereadily available at the divider output despite quadrature phaseinaccuracies at the output of the VCO. Assume that the VCO outputs havephase of 0 and 90°+q, where q is ideally 0, and that the dividerproduces perfect quadrature outputs. At the LO generator outputs thefollowing signals exist:

V _(out) ^(_(—)) _(Q)=Cos(ω₂ t)·Cos(ω₁ t+θ)−Sin(ω₂ t)·Sin(ω₁ t)  (50)

[0269] and

V _(out) ^(_(—)) _(Q)=Cos(ω₂ t)·Sin(ω₁ t)+Sin(ω₂ t)·Cos (ω₁ t+θ)  (51)

[0270] where ω₁ is the VCO radian frequency, and ω₂ is the dividerradian frequency, equal to 0.5 ω₁. By simplifying equation (25) andequation (26), the signals at the output of mixers will be:$\begin{matrix}{\begin{matrix}{V_{out\_ I} = {{{- {{Sin}\left( \frac{\theta}{2} \right)}} \cdot {{Sin}\left( {{\left( {\omega_{1} - \omega_{2}} \right)t} + \frac{\theta}{2}} \right)}} +}} \\{{{{Cos}\left( \frac{\theta}{2} \right)} \cdot {{Cos}\left( {{\left( {\omega_{1} + \omega_{2}} \right)t} + \frac{\theta}{2}} \right)}}}\end{matrix}{and}} & (52) \\\begin{matrix}{V_{out\_ Q} = {{{- {{Sin}\left( \frac{\theta}{2} \right)}} \cdot {{Cos}\left( {{\left( {\omega_{1} - \omega_{2}} \right)t} + \frac{\theta}{2}} \right)}} +}} \\{{{{Cos}\left( \frac{\theta}{2} \right)} \cdot {{Sin}\left( {{\left( {\omega_{1} + \omega_{2}} \right)t} + \frac{\theta}{2}} \right)}}}\end{matrix} & (53)\end{matrix}$

[0271] The above equations show that regardless of the value of θ, theoutputs are always in quadrature. However, other effects should beevaluated. First, a spur at ω₁−ω₂=0.5 ω₁ is produced at the output. Thisspur can be attenuated by 2×22=44 dB by the LC filters at the mixer andits buffer outputs. Thus, for 60 dB rejection, the single sidebandmixers need to provide an additional 16 dB of rejection (about 0.158).Based on equation (53), tan(θ/2)=0.158, or θ≈18°, phase accuracy ofbetter than 18° can generally be achieved. Second, phase error at theVCO output lowers the mixer gain (term Cos(θ/2) in equation (52) or(53)). For a phase error of 18°, the gain reduction is, however, only0.1 dB, which is negligible. For θ=90° (a single-phase VCO), bothsidebands are equally upconverted at the mixer output. However, the LCfilters reject the lower sideband by about 44 dB. The mixer gain willalso be 3 dB lower. This will slightly increase the power consumption ofthe LO generator. If θ=180° (the VCO I and Q outputs are switched), thelower sideband is selected, and the desired sideband is completelyrejected.

[0272] Similarly, the LO generator will not be sensitive to the phaseimbalance of the divider outputs if the VCO is ideal. However, if thereis some phase inaccuracy at both the divider and VCO outputs, the LOgenerator outputs will no longer be in quadrature. In fact, if the VCOoutput has a phase error of q₁ and the divider output has a phase errorof q₂, the LO generator outputs will be: $\begin{matrix}{\begin{matrix}{V_{out\_ I} = {{{- {{Sin}\left( \frac{\theta_{1} - \theta_{2}}{2} \right)}} \cdot {{Sin}\left( {{\left( {\omega_{1} - \omega_{2}} \right)t} + \frac{\theta_{1} - \theta_{2}}{2}} \right)}} +}} \\{{{{Cos}\left( \frac{\theta_{1} - \theta_{2}}{2} \right)} \cdot {{Cos}\left( {{\left( {\omega_{1} + \omega_{2}} \right)t} + \frac{\theta_{1} - \theta_{2}}{2}} \right)}}}\end{matrix}{and}} & (54) \\\begin{matrix}{V_{out\_ Q} = {{{- {{Sin}\left( \frac{\theta_{1} - \theta_{2}}{2} \right)}} \cdot {{Cos}\left( {{\left( {\omega_{1} - \omega_{2}} \right)t} + \frac{\theta_{1} - \theta_{2}}{2}} \right)}} +}} \\{{{{Cos}\left( \frac{\theta_{1} - \theta_{2}}{2} \right)} \cdot {{Sin}\left( {{\left( {\omega_{1} + \omega_{2}} \right)t} + \frac{\theta_{1} - \theta_{2}}{2}} \right)}}}\end{matrix} & (55)\end{matrix}$

[0273] This shows that the outputs still have phases of 0 and 90°, buttheir amplitudes are not equal. The amplitude imbalance is equal to:$\begin{matrix}\begin{matrix}{\frac{\Delta \quad A}{A} = {2\frac{{{Cos}\left( \frac{\theta_{1} + \theta_{2}}{2} \right)} - {{Cos}\left( \frac{\theta_{1} - \theta_{2}}{2} \right)}}{{{Cos}\left( \frac{\theta_{1} + \theta_{2}}{2} \right)} + {{Cos}\left( \frac{\theta_{1} - \theta_{2}}{2} \right)}}}} \\{= {2{\tan \left( \frac{\theta_{1}}{2} \right)} \times {\tan \left( \frac{\theta_{2}}{2} \right)}}}\end{matrix} & (56)\end{matrix}$

[0274] If θ₁ and θ₂ are small and have an equal standard deviation, thatis, the phase errors in the VCO and divider are the same in nature, thenthe output amplitude standard deviation will be: $\begin{matrix}{\sigma_{A} \approx \frac{\left( \sigma_{\theta} \right)^{2}}{2}} & (57)\end{matrix}$

[0275] where σ_(A) is the standard deviation of the output amplitude,and σ_(θ) is the phase standard deviation in radians. Equation (57)denotes that the phase inaccuracy in the VCO and divider has a secondorder effect on the LO generator. For instance, if θ₁ and θ₂ are on thesame order and about 10°, the amplitude imbalance of the output signalswill be only about 1.5%. In this case, the lower sideband will be about15 dB rejected by the mixers, which will lead to a total attenuation ofabout 22+22+15=59 dB. This shows that the LO generator is robust tophase errors at the VCO or divider outputs, since typically phase errorsof less than 5° can be obtained on chip.

[0276] Phase errors in the divider can originate from the mismatch atits output Moreover, for N=2, if the input of the divider does not havea 50% duty cycle, the outputs will not be in quadrature. Again, thedeviation from a 50% duty cycle in the divider input signal may becaused due to mismatch. Typically, with a careful layout, this mismatchis minimized to a few percent. The latter problem can also be alleviatedby improving the common-mode rejection of the buffer preceding thedivider (888 in FIG. 33). One possible way of doing so is to add a smallresistor at the common tail of the inductors in the buffer. For adifferential output, this resistor does not load the resonator at thebuffer output, since the inductors common tail is at AC ground. Acommon-mode signal at the output is suppressed however, since thisresistor degrades the LC circuit quality factor. The value of theresistor should be chosen appropriately so as not to produce a headroomproblem in the buffer.

[0277] Embodiments of the present invention that are fully integratedonto a single IC can be implemented with a wide tuning range VCO withconstant gain. In a typical IC process, the capacitance can vary by 20%.This translates to a 10% variation in the center frequency of theoscillator. A wide tuning range can be used to compensate for variation.Variations in temperature and supply voltage can also shift the centerfrequency. To generate a wide tuning range, two identical oscillatorscan be coupled together as shown in FIG. 34. This approach forces theoscillation to be dependent on the amount of coupling between the twooscillators.

[0278] In the described exemplary embodiment of the VCO shown in FIG.34, the tuning curve is divided into segments with each segmentdigitally selected. This approach ensures a sufficient amount ofcoupling between the two oscillators for injection lock. In addition,good phase noise performance is also obtained. The narrow frequencysegment prevents the gain of the VCO from saturating. The segmentationlowers the VCO gain by the number of segments, and finally by scalingthe individual segments, a piecewise linear version of the tuning curveis made resulting in a constant gain VCO.

[0279]FIG. 34 shows a block diagram of the wide tuning range VCOcomprising two coupled oscillators where the amount of couplingtransconductance is variable. The wide tuning range VCO comprises tworesonators 800, 802 and four transconductance cells, g_(m) cells 804,806, 808, 810. The transconductance cells are driver that convertsvoltage to current The transconductance cells used to couple theoscillators together have a variable gain. The first VCO 800 providesthe I signal and the second VCO provides the Q signal. The output of thefirst VCO 800 and the output of the second VCO 802 are coupled totransconductance cells 806, 807, respectively, combined, and fed back tothe first VCO 800. The transconductance cell 807 used for feeding backthe output of the second VCO to the first VCO is a programable variablegain cell. Similarly, the output of the second VCO 802 and the output ofthe first VCO 800 are coupled to transconductance cells 805, 804,respectively, combined, and fed back to the second VCO 802. Thetransconductance cell 804 used for feeding back the output of the firstVCO to the second VCO is a programmable variable gain cell. The gain ofthe programmable variable gain transconductance cells 804, 807 can bedigitally controlled from the controller

[0280]FIG. 35 shows a schematic block diagram of the wide-tuning rangeVCO described in connection with FIG. 34. The wide-tuning range VCOincludes individual current sources 810, 812, 814, 816, cross-coupledtransistors 818, 820 with resonating inductors 826, 828, andcross-coupled transistors 822, 824 with resonating inductors 830, 832.Two differential pairs couple the two sets of oscillators. Differentialpair 834, 836 are coupled to the drains of transistors 824, 822,respectively. Differential pair 838, 840 are coupled to the drains oftransistors 818, 820. Tank #1 comprises inductors 826 and 828. Tank #2comprises inductors 830 and 832.

[0281] Transistors 818 and 820 form a cross-coupled pair that injects acurrent into tank #1 in which the current through the transistor 818 isexactly 180 degrees out of phase with the current in the transistor 820.Likewise, transistors 822 and 824 form a cross-coupled pair that injectsa current into tank #2 in which the current through the transistor 822is exactly 180 degrees out of phase with the current in the transistor824. The first set of coupling devices 834, 836 injects a current intotank #1 that is 90 degrees out of phase with current injectedrespectively by the transistors 818, 820. The second set of couplingdevices 838, 840 injects a current into tank #2 that is 90 degrees outof phase with the current injected respectively by the transistors 822,824. The tank impedances causes a frequency dependent phase shift. Byvarying the amplitude of the coupled signals, the frequency ofoscillation changes until the phase shift through the tanks results in asteady-state solution. Varying the bias of the current source controlsthe gm of the coupling devices. Current sources 812, 816 provide controlof VCO tuning. Current sources 810, 814 provide segmentation of the VCOtuning range.

[0282]FIG. 36(a) shows the typical tuning curve of the wide tuning rangeVCO before and after segmentation. The horizontal axis is voltage. Thevertical axis is frequency. FIG. 36(b) shows how segmentation is used todivide the tuning range and linearize the tuning curve. The lineartuning curves correspond to different VCO segments. The slope of thelinear tuning curves is a result control of VCO tuning. The horizontalaxis is voltage. The vertical axis is frequency.

[0283]FIG. 37(a) shows how the VCO of FIG. 34 can be connected to thedivider before being upconverted to the RF clock frequency in the LOgenerator. The I output signal of the VCO is coupled to buffer 884 andthe Q output signal of the VCO is coupled to buffer 886. Buffer 888combines the I-Q data from the buffer 884 and the buffer 886 to obtain alarger signal. The large signal is coupled to a divider 50 where it isdivided in frequency by N to get quadrature signals.

[0284] In another embodiment of the present invention, a polyphasefilter 892 follows a single-phase VCO as shown in FIG. 37(b). Thisapproach uses a single phase VCO 48 with a polyphase filter 892 to getquadrature signals. The output of the VCO 48 is coupled to a buffer 888.The buffer provides sufficient drive for the polyphase filter 892.

[0285] A multiple stage polyphase filter can be used to obtain betterphase accuracy at a certain frequency range. Embodiments of the presentinvention that are fully integrated into a single IC, the requiredfrequency range is mainly set by the process variation on the chip andthe system bandwidth.

[0286] Any amplitude imbalance in the signals at the VCO and divideroutput will only cause a second order mismatch in the amplitude of theLO generator signals, and the output phase will remain 0 and 90°. If thestandard deviation of the amplitude imbalance at the VCO and divider arethe same and equal to ca, then the standard deviation of the LOgenerator output amplitude imbalance (σ_(A)) will be: $\begin{matrix}{\sigma_{A} = \frac{\left( \sigma_{\alpha} \right)^{2}}{2}} & (58)\end{matrix}$

[0287] The reason phase inaccuracy is more emphasized here is thatbecause of the limiting stages in the LO generator and the hardswitching at the mixers LO input, most of the errors will be in phase,rather than amplitude.

[0288] Although the phase or amplitude inaccuracy at the mixers input orLO has only a second order effect on the LO generator, any mismatch atthe mixers outputs or the following stages will directly cause phase andamplitude imbalance in the LO generator outputs. This mismatch willtypically be a few percent, and will not adversely impact thetransceiver performance, since in a low-IF or direct conversionarchitectures the required image rejection is usually relaxed.

[0289] 4.0 Controller

[0290] The controller performs adaptive programming and calibration ofthe receiver, transmitter and LO generator (see FIG. 2). An exemplaryembodiment of the controller in accordance with one aspect of thepresent invention is shown in FIG. 38. A control bus 17 provides two waycommunication between the controller and the external processing device(not shown). This communication link can be used to externally programthe transceiver parameters for different modulation schemes, data ratesand IF operating frequencies. In the described exemplary embodiment, theexternal processing device transmits data across the control bus 17 to abank of addressable registers 900-908 in the controller. Eachaddressable register 900-908 is configured to latch data for programmingone of the components in the transmitter, receiver LO generator. By wayof example, the power amplifier register 900 is used to program the gainof the power amplifier 62 in the transmitter (see FIG. 2). The LOregister 902 is used to program the IF frequency in the LO generator.The demodulator register 903 is used to program the demodulator for FSKdemodulation, or alternatively in the described exemplary embodiment,program the A/D converter to handle different modulation schemes. TheAGC register 905 programs the gain of the programmable multiple stageamplifier when in the AGC mode. The filter registers 901, 904, 906program the frequency and bandwidth of their respective filters.

[0291] The transmission of data between the external processing deviceand the controller can take on various forms including, by way ofexample, a serial data stream parsed into a number of data packets. Eachdata packet includes programming data for one of the transceivercomponents accompanied by a register address. Each register 900-908 inthe controller is assigned a different address and is configured tolatch the programming data in the each data packet where the registeraddress in that data packet matches its assigned address.

[0292] The controller also may include various calibration circuits. Inthe described exemplary embodiment, the controller is equipped with anRC calibration circuit 907 and a bandgap calibration circuit 908. The RCcalibration circuit 907 can compensate an integrated circuit transceiverfor process, temperature, and power supply variations. The bandgapcalibration circuit can be used by the receiver, transmitter, and LOgenerator to set amplifier gains and voltage swings.

[0293] The programming data from the addressable registers 900-908 andthe calibration data from the RC calibration circuit 907 and the bandgapcalibration circuit 908 are coupled to an output register 909. Theoutput register 909 formats the programmability and calibration datainto a data packets. Each data packet includes a header or preamblewhich addresses the appropriate transceiver component The data packetsare then transmitted serially over a controller bus 910 to their finaldestination. By way of example, the output register 909 packages theprogramming data from the power amplifier register 900 with the headeror preamble for the power amplifier and outputs the packaged data as thefirst data packet to the controller bus 910.

[0294] The second data packet generated by the output register 909 isfor the programmable low pass filter in the transmitter. The second datapacket includes two data segments each with its own header or preamble.The first segment consists of both programmability and calibration data.Because the programmability feature requires a large dynamic range asfar as programming the programmable low pass filter to handle differentfrequency bands, and the calibration feature is more of a fine tuningfunction of the programmable low pass filter once tuned requiring a muchsmaller dynamic range, a single digital word containing both programmingand calibration information can be used with the most significant bits(MSB) having the programming information and the least significant bits(LSB) having the calibration information. To this end, the outputregister 909 combines the output of the low pass filter register 901with the output of the RC calibration circuit 907 with the low passfilter register output constituting the MSBs and the RC calibrationcircuit output constituting the LSBs. A header or preamble is attachedto the combined outputs identifying the data packet for RC calibrationof the programmable low pass filter in the transmitter. Similarly, thesecond segment of the second data packet is generated by combining thelow pass filter register output (as the MSBs) with the bandgapcalibration circuit output (as the LSBs) and attaching a header orpreamble identifying the data packets for bandgap calibration of theprogrammable low pas filter.

[0295] The third data packet generated and transmitted by the outputregister 909 can program the dividers in the LO generator to producedifferent IF frequencies. The third data packet can be a single segmentof data with a header or preamble identifying the LO generator forprogramming each divider. Alternatively, the third data packet caninclude any number of data segments with, in one embodiment, differentprogramming data for each divider in the LO generator. Each data segmentwould include a header or preamble identifying a specific divider in theLO generator.

[0296] The fourth data packet generated and transmitted by the outputregister 909 could include the programming data output from thedemodulator register 904 with the appropriate header or preamble.

[0297] The output of the complex bandpass filter register 904 can becombined with the output from the RC calibration circuit 907 to form thefirst segment of the fifth data packet. The output of the complexbandpass filter register 904 can also be combined with the output of thebandgap calibration circuit 908 to form the second segment of the fifthdata packet. Each segment can have its own header or preamble indicatingthe type of calibration data for the complex bandpass filter.

[0298] The sixth data packet generated and transmitted by the outputregister 909 can be the output data from the AGC register 905accompanied by a header or preamble identifying the data packet for theprogrammable multiple stage amplifier in the receiver.

[0299] The output of the polyphase filter register 906 can be combinedwith the output from the RC calibration circuit 907 to form the firstsegment of the seventh data packet. The output of the polyphase filterregister 906 can also be combined with the output of the bandgapcalibration circuit 908 to form the second segment of the seventh datapacket. Each segment can have its own header or preamble indicating thetype of calibration data for the polyphase filter.

[0300] Finally, the output register 907 can configure additional datapackets from the output of the RC calibration circuit 907 and, inseparate data packets, the output of the bandgap calibration circuit 908with appropriate headers or preambles.

[0301] As those skilled in the art will appreciate, other datatransmission schemes can be used. By way of example, the separate outputregisters for each transceiver component could be used. In thisembodiment, each output register would be directly connected to one ormore transceiver components.

[0302] 4.1 RC Calibration Circuit

[0303] RC calibration circuits can provide increased accuracy forimproved performance. Embodiments of the present invention that areintegrated into a single IC can utilize RC calibration to compensate forprocess, temperature, and power supply variation. For example,variations in the absolute value of the RC circuit in a complex filtercan limit the amount of rejection that the filter can provide. In thedescribed exemplary embodiments of the present invention, an RCcalibration circuit in the controller can provide dynamic calibration ofevery RC circuit by providing a control word to the transmitter,receiver and LO generator.

[0304]FIG. 39 shows an exemplary RC calibration circuit in accordancewith an embodiment of the present invention. The calibration circuituses the reference clock from the LO generator to generate a 4-bitcontrol word using a compare-and-increment loop until an optimum valueis obtained. The 4-bit control provides an efficient technique forcalibrating the RC circuits of the transceiver with a maximum deviationfrom its optimal value of only 5%.

[0305] Transistors 172, 174, 176. 178, 180, 182 form a cascode currentsource with a reference current I_(REF) 184. With the gates of thetransistors 172 and 178 tied to their respective sources, a fixedreference current I_(REF) 184 can be established. By tying the gates ofthe transistors 174, 180 to the gates of the transistors 172, 178,respectively, the current through resistor R_(C) 186 can be mirrored toI_(REF) 184. Similarly, by tying the gates of the transistors 176, 182to the gates of the transistors 174, 180, respectively, the currentthrough resistor R_(C) 186 can be mirrored to a tunable capacitor C_(C)188. The calibration circuit tunes the absolute value of the R_(C) to adesired frequency by using this cascode-current source to provideidentical currents to the on-chip reference resistor R_(C) 186 and tothe tunable capacitor C_(C) 188 generating the voltages V_(RES) 190 andV_(CAP) 192, respectively. Embodiments of the present invention that areintegrated into a single IC can use an off-chip reference resistor R_(c)to obtain greater calibration accuracy. The current through the tunablecapacitor is controlled by a logic control block 195 via switch S₂ 193.During the charging phase, switch S₂ 193 is closed and switch S is opento charge the tunable capacitor C_(C) 188 to V_(CAP). The voltage heldon the tunable capacitor 188 V_(CAP) is then compared, using a latchedcomparator 198, to a voltage generated across the reference resistor186. The value of the tunable capacitor C_(c) 188 is incremented insuccessive steps by the logic control block 195 until the voltage heldby the tunable capacitor C_(C) matches the voltage across the referenceresistor 186, at which point the 4-bit control word for optimalcalibration of the RC circuits for the transmitter, receiver, and LOgenerator is obtained. More particularly, once the voltage V_(CAP)reaches the voltage V_(RES), the output of the comparator output 198switches. The switched comparator output is detected by the controllogic 195. The control logic 195 opens switch S₂ 193 and closes switchS₁ 194 causing the tunable capacitor 188 C_(C) to discharge. Theresultant 4-bit control word is latched by the control logic 195 andcoupled to the transceiver, receiver, and LO generator.

[0306] C_(p) 200 compensates for the parasitic capacitance loading ofthe capacitive branch. By choosing C_(c) 188 to be much larger thanC_(p) 200, the voltage error at node V_(CAP) 192 caused by charging theparasitic capacitance becomes negligible.

[0307] The clock signals used by the calibration circuit are generatedby first dividing the reference clock down in frequency, and thenconverting the result into different phases for the charging,comparison, increment, and discharging phases of calibration.Embodiments of the present invention that are integrated onto a singleIC can obtain an accurate RC value because capacitor scaling andmatching on the same integrated circuit can be well-controlled withproper layout technique. The described RC calibration circuit providesan RC-tuning range of approximately +40%, which is sufficient to coverthe range of process variation typical in semiconductor fabrication.

[0308] 4.2 RC Calibration Circuit Using Polyphase Filtering

[0309] An RC calibration circuit using polyphase filtering is analternative method for calibrating RC circuits in the transmitter,receiver, and LO generator. The RC calibration using polyphase filteringcircuit includes an auto-calibration algorithm in which the capacitorsor the RC circuits in the transceiver, receiver and LO generator can becalibrated with a control word generated by comparing the signalattenuation across two tunable polyphase filters. The calibrated RCvalue obtained as a result of this algorithm is accurate to within ±5%of its optimal value.

[0310]FIG. 40 shows an exemplary embodiment of the RC calibrationcircuit using polyphase filtering. The RC calibration circuit uses thereference clock from the LO generator to adjust the RC value in twopolyphase filters 280, 282 in successive steps until an optimum valuehas been selected. In this process, the two polyphase filters 280, 282provide signal rejection that is dependent upon the value of ω=(RC)⁻¹ towhich they are tuned by control logic 286. Initially, the first filter(Polyphase A) 280 is tuned to a frequency less than the frequency of thereference clock (reference frequency), and the second filter (PolyphaseB) 282 is tuned to a frequency greater than the reference frequency bycontrol logic 286. The signals at the outputs of the polyphase filtersare detected with a received-signal-strength-indicator (RSSI) block 284,285 in each path. A filter is coupled to RSSI block 284 and thepolyphase B filter is coupled to RSSI block 285.

[0311] With an input dynamic range of 50 dB, the RSSI circuit isdesigned to detect the levels of rejection provided by the polyphasefiltering. The outputs of RSSI block 284 and RSSI block 285 are coupledto a comparator 280 where the level of signal rejection of eachpolyphase filter is compared by comparator 280. The outputs of the RSSIblocks are also coupled to the control logic 286. The control logic 286determines from the RSSI outputs which polyphase filter has a loweramount of signal suppression. Then, the control logic 286 adjusts thefrequency tuning of that filter in an incremental step via the controllogic 286. This is done by either increasing the tuned frequency of thefirst filter (polyphase A) filter 280, or by decreasing the tunedfrequency of the second filter (polyphase B) 282 by changing theappropriate 4-bit control word. This process continues in successivesteps until the 4-bit control word in each branch are identical, atwhich point, the RC values of the two polyphase filters are equal. The4-bit control word provides a maximum deviation of only ±5%.

[0312] In the described exemplary embodiment, the frequency of the inputsignal X_(IN) is derived from the reference frequency and is chosen tobe, by way of example, 2 MHz This input signal X_(IN) is obtained byinitially dividing the reference clock down in frequency, followed by aconversion into quadrature phases at the control logic 286. By dividingthe reference clock by a factor greater than two with digital flip-flops(not shown), the input signal at X_(IN) is known to be differential withwell-defined quadrature phases.

[0313] Two branches of polyphase filtering are used in this algorithm.Two 4-bit control words are used to control the value of thecapacitances in each polyphase filter. The initial control words set thecapacitance in the first filter (Polyphase A) to its maximum value andthe capacitance in the second filter (Polyphase B) to its minimum value.This provides an initial condition in which the filters have maximumsignal suppression set at frequencies (ω_(low) and ω_(high)) that areapproximately ±40% of the frequency of the input signal X_(IN) for thecase of nominal process variation For a sinusoidal input X_(IN), thecalibration circuit depicted in FIG. 40 would require only asingle-stage polyphase filter in each branch. The single-stage filterswould attenuate the sinusoid input signal, generating outputs at X_(A)and X_(B) with the dominant one still at the same frequency as the inputsignal. However, the reference clock from the LO generator is a digitalrail-to-rail clock. Because the input is not a pure sinusoid,multiple-stage filters may provide greater calibration accuracy. In thecase of a single-stage filter with a digital clock, the filter wouldsuppress the fundamental frequency component at ω_(in) to a significantdegree but the harmonics would pass through relatively unaffected. TheRSSI block would then detect and limit the third harmonic component ofthe input signal at 3ω_(in), as it becomes the dominant frequencycomponent after the fundamental is suppressed. This could result in aninaccurate calibration code.

[0314] A three-stage polyphase filter can be used in each branch tosuppress the fundamental frequency component of X_(IN) as well as the3rd and 5th harmonics. The first stage of the polyphase filter canprovide rejection of the fundamental frequency component. The secondstage can provide rejection of the 3rd harmonic. The third stage canprovide rejection of the 5th harmonic. At the same time, the higherharmonics of the input signal X_(IN) can be suppressed with an RClowpass filter in a buffer (not shown) preceding the polyphase filters.As a result, the dominant frequency component of the signals X_(A) andX_(B) remains at the input frequency ω_(in), which is then properlydetected by the RSSI blocks.

[0315] A calibration clock used for the control logic runs at afrequency of 250 kHz The reference clock can be divided down inside thecontroller, or alternatively in the control logic. This clock frequencyhas been selected to allow the RSSI outputs to settle after thecapacitance value in one of the polyphase filters has been incrementedor decremented. For a clock frequency of 250 kHz and a 4-bit controlword generating 2⁴ possible capacitance values, the calibration iscompleted within (250 kHz)⁻¹(2⁴−1)=60 μs. During the calibration processthe calibration circuitry draws 4 mA from a 3-V supply, and the RCcalibration circuitry can be powered down when the optimal RC value hasbeen selected to reduce power consumption.

[0316] 4.3 The Capacitor Array

[0317] In the transmitter, receiver and LO generator,metal-insulator-metal (MIM) capacitors can be used as the calibrationcomponent for the RC circuits. As those skilled in the art willappreciate, other capacitor technologies may be used. The MIM capacitorsare generally characterized by a low bottom-plate parasitic capacitanceto substrate of 1%.

[0318] A parallel capacitor array can be used in calibrating each RCcircuit as shown in FIG. 41. The parallel array is much smaller in areathan a series array for the same capacitor value.

[0319] Complementary MOS switches or other switches known in the art,can be used in the capacitor array. The capacitor array can include anynumber of capacitors. In the exemplary embodiment, the capacitor arraycapacitors 290, 292, 294, 296, 298 are connected in parallel. Switches300, 302, 304, 306 are used to switch the capacitors 292, 294, 296, 298,respectively, in and out of the capacitor array. In the describedembodiment, capacitor 290 is 2.4 pF, capacitor 292 is 2.4 pF, capacitor294 is 1.2 pF, capacitor 296 is 0.6 pF, capacitor 298 is 0.3 pF. Theswitch positions are nominally selected to produce an equivalentcapacitance equal to 4.8 pF. A code of “0111” means that capacitors 294,296, 298 are switched out of the capacitor array and capacitors 290, 292are in parallel.

[0320] The switches can be binary-weighted in size and the switch sizescan be chosen according to tradeoffs regarding parasitic capacitancesand frequency limitations based on the on-resistance of the CMOSswitches. The capacitive error resulting from the parasitic capacitancein each capacitive array does not result in frequency error between thethree polyphase stages of the RC calibration circuit in the controller.This is because by using same capacitor array in each filter, and byscaling the resistance accordingly in each case. Scaling resistances,relative to those in the fundamental polyphase filter, by factors of ⅓and ⅕ in the 3^(rd) and 5^(th) harmonic filters respectively, areachieved with a high degree of accuracy with proper layout Similarly, RCtuning in all other blocks utilizing the calibrated code is optimizedwhen an identical capacitive array is used, scaling only the resistancevalue in tuning to the desired frequency. The capacitors in thecapacitive arrays are laid out in 100 fF increments to improve thematching and parasitic fringing effects.

[0321] 4.4 Bandgap Calibration Circuit for Accurate Bandgap ReferenceCurrent

[0322] In accordance with an exemplary embodiment of the presentinvention, a bandgap reference current is generated by a bandgapcalibration circuit. The bandgap reference current is used by thereceiver, transmitter, and LO generator to set amplifier gains andvoltage swings. The bandgap calibration circuit generates an accuratevoltage and resistance. An accurate bandgap reference current resultsfrom dividing the accurate voltage by the an accurate resistance.

[0323] Bandgap calibration circuits can provide increased accuracy forimproved performance. Embodiments of the present invention that areintegrated onto a single IC can utilize bandgap calibration circuits tocompensate for process, temperature, and power supply variations. Forexample, variations in the absolute value of the resistance in a bandgapreference may result in deviations from optimal performance in sensitivecircuitry that rely on accurate biasing conditions. In the describedexemplary embodiment of the transceiver, a bandgap calibration circuitin the controller 16 provides an effective technique forself-calibration of resistance values in the transmitter, receiver andLO generator. The calibrated resistance values obtained as a result ofthe algorithm employed in the bandgap calibration circuit generate abias current that varies by only +2% over typical process, temperature,and supply variation.

[0324] Embodiments of the present invention which are integrated into asingle IC can use the described bandgap calibration circuit to provideaccurate on-hip resistors by comparing the on-hip resistances to anoff-hip reference resistor with a low tolerance of 1%. Using thismethod, trimming of on-hip resistance values with a total tolerance of2% can be achieved.

[0325]FIG. 42 shows an exemplary embodiment of the bandgap calibrationcircuit. The bandgap calibration circuit uses the reference clockprovided from the LO generator and a reference resistor R_(REF) 236 toadjust a tunable resistance value R_(POLY) 238 in acompare-and-increment loop until an optimum value is obtained. Inembodiments of the present invention which are integrated into a singleIC, the reference resistor R_(REF) 236 can be off-chip to provideimproved calibration accuracy. A 4-bit control word is output toaccurately calibrate the resistors in the transmitter, receiver and LOgenerator within ±2%. Transistors 227, 226, 228, 230, 232, 234 form acascode current with a reference current I_(REF). The transistors 224,230 each have their gates tied to their respective sources to set up thereference current I_(REF). By tying the gates of the transistors 224,230, respectively to the gates of the transistors 226, 232, thereference current I_(REF) is mirrored to the reference resistorR_(REF 236). Similarly, by tying the gates of the transistors 228, 234,respectively to the gates of the transistors, the reference currentI_(REF) is also mirrored to the tunable resistor R_(POLY) 238. Thevoltage generated across the tunable resistor R_(POLY) 238 is compared,using a latched comparator 240, to the voltage generated across thereference resistor R_(REF) 236. The value of the tunable resistorR_(POLY) 236 is incremented in successive steps, preferably, every 0.5μs, through the utilization of control logic 242 that is clocked, by wayof example, at 2 MHz This process continues until the voltage V_(POLY)across the tunable resistor R_(POLY) 238 matches the voltage V_(REF)across the off-chip reference resistor R_(REF) 236 causing the output ofthe comparator to change states and disable the control logic 242. Oncethe control logic is disabled, the 4-bit control word can be used toaccurately calibrate the resistors in the transmitter, receiver and LOgenerator.

[0326] The clock signals used by the calibration circuit are generatedby first dividing the reference clock input into the controller from theLO generator down in frequency, and then converting the result intodifferent phases for the comparison and increment phases of calibration.This bandgap calibration circuit provides accurate resistance values foruse in various on-chip circuit implementations because resistor scalingand matching on the same integrated circuit can be well controlled withproper layout techniques. The bandgap calibration circuit provides aresistor tuning range of approximately +30%, which is sufficient tocover the range of process variation typical in semiconductorfabrication. With a 4-bit control word generating 24 possible resistancevalues, the calibration is completed within (2 MHz)−1(24−1)=7.5 ms. Thecalibration circuit can be powered down when the optimal resistancevalue has been obtained.

[0327] The bandgap calibration circuit can be used for numerousapplications. By way of example, FIG. 43 shows a bandgap calibrationcircuit 244 used in an application for calibrating a bandgap referencecurrent that is independent of temperature. The 4-bit control word fromthe bandgap calibration circuit is coupled, by way of illustration, tothe receiver. The 4-bit control word is used to calibrate resistances ina proportional-to-absolute-temperature (PTAT) bias circuit 246, and alsoin a V_(BE) (negative temperature coefficient) bias circuit 248. Theoutputs of these blocks are two bias voltages, V_(P) 250 and V_(N), 252that generate currents exhibiting a positive temperature coefficient,and a negative temperature coefficient, respectively. When thesecurrents are summed together using the cascode current mirror formed bytransistors 254, 256, 258, 260, the result is a current I_(OUT) displaysa (ideally) zero temperature coefficient.

[0328] 4.5 Resistor Array

[0329] In the transmitter, receiver and LO generator non-silicidedpolysilicon resistors can be used. As those skilled in the art willappreciate, other resistor technologies can also be used. Non-silicidedpolysilicon resistors have a high sheet resistance of 200-Ω/square alongwith desirable matching properties. A switching resistor array as shownin FIG. 44 can be used to calibrate a resistor. The array includesserial connected resistors 208, 210, 212, 214, 216, which, by way ofexample, have resistances of 2200 Ω, 1100Ω, 550 Ω, 275 Ω, and 137 Ω,respectively. The resistors 210, 212, 214, 216 include a bypass switchfor switching the resistors in and out of the array. The switchpositions are nominally selected to produce an equivalent of 3025 Ω.This resistance value has been chosen as a convenience to match thevalue used in generating an accurate bandgap reference current A 4-bitcalibration code 206 is used to control the total resistance in thisarray. As seen in FIG. 44, the resistances are binary-weighted in valueand the accurate scaling of each incremental resistance results byplacing the largest resistor (2200 Ω) 208 in series to generate eachvalue. In the described embodiment, the incremental resistances shown inFIG. 44 are chosen so that the total resistance in the array covers arange 30% above and below its nominal value, with a maximum resistanceerror of +2% determined by the incremental resistance switched by theLSB. The range of resistance covered by the array is sufficient to covertypical process variations in a semiconductor process. A seriesresistive array may be desirable opposed to a parallel resistive arraybecause of the smaller area occupied on the wafer.

[0330] CMOS switches are one of several different types of switchtechnology that can be used. The sizing of the switches entails atradeoff between the on-resistance of each switch and the frequencylimitations that result from the parasitic capacitances associated witheach switch. For calibration resistors in the bandgap referencecircuits, large switches are used to minimize the effect of theon-resistance of each switch, as frequency limitations are not a concernfor this application.

[0331] 5.0 Floating MOSFET Capacitors

[0332] Embodiments of the present invention that are integrated into asingle IC can be implemented with a variety of technologies including,by way of example, CMOS technology. Heretofore, CMOS capacitors betweentwo nodes with similar voltages (i.e., floating capacitors) have beenproblematic. In the described exemplary embodiment of the presentinvention, a MOS capacitor is used between two nodes having similarvoltages for signals with no DC information. The capacitor is made oftwo MOS capacitors in series with a large resistor in between to groundfor biasing.

[0333]FIG. 45 is a block diagram of the Floating MOS capacitor inaccordance with an embodiment of the present invention. As shown in FIG.45, the capacitor comprises two similar devices 858, 860 in series. EachMOS transistor has its source and drain connected together. Theconnected drain-source terminal of the MOS transistor 858 constitutesthe input of the CMOS capacitor and the connected drain-source terminalof the MOS transistor 860 constitutes the output of the CMOS capacitor.The gates of each MOS transistor are connected through a common resistor862 to a bias source (not shown).

[0334] 6.0 Duplexing

[0335] In an alternative embodiment of the present invention, anintegrated matching circuit can be used to connect the LNA in thereceiver to the PA in the transmitter. As the level of integration inradio communication circuits tend to grow, more functions are embodiedon the same chip and off-chip components are used less than ever.Presence of external components not only augments the manufacturingcosts, but also increases the pin count on the main chip. The antennaswitch is an example of such components. This switch is used to connectthe receiver to antenna in reception mode and the transmitter to antennain transmission mode. In the described exemplary embodiment of thepresent invention, the antenna switch can be eliminated, and the inputof the receiver can be tied to the output of the transmitter. Thisapproach has various applications including, but not limited to, singlechip integration.

[0336] Since the antenna is usually single-ended, differentialapplications generally require a mechanism to convert the antenna signalfrom single-ended to differential for connection to the differential lownoise amplifier (LNA) or the differential PA. The circuit implementationfor a single-ended to differential LNA is shown in FIGS. 46 and 47. LCcircuit, 646, 648 and the CL circuit 652, 650 matches the PA to theantenna when the PA is on and the LNA is off(as shown in FIG. 46), andmatches the LNA to the antenna when the LNA is on and the PA is off (asshown in FIG. 47). Since the LNA is off and it only introduces acapacitive loading to the PA. The matching circuit can be designed tocompensate for this additional capacitance.

[0337] In operation, during the transmit mode, a differential voltageacross the drains of the PA transistors 634, 632 is generated. The twodrains assert 180-degree out of phase voltages and they are combinedthrough the LC and CL matching circuits to yield a single-ended voltageat the output. The LC circuit shifts the phase of the output signal fromthe transistor 634 by 90 degrees. The CL circuit shifts the phase of thesignal output from the transistor 632 by 90 degrees in the oppositedirection. Consequently, both signals are in-phase when combined at theoutput of te matching circuits.

[0338] Although a preferred embodiment of the present invention has beendescribed, it should not be construed to limit the scope of the appendedclaims. For example, the present invention can be into a singleintegrated circuit, can be constructed from discrete components, or caninclude one or more integrated circuits supported by discretecomponents. Those skilled in the art will understand that variousmodifications may be made to the described embodiments. Moreover, tothose skilled in the various arts, the invention itself herein willsuggest solutions to other tasks and adaptations for other applications.It is therefore desired that the present embodiments be considered inall respects as illustrative and not restrictive, reference being madeto the appended claims rather than the foregoing description to indicatethe scope of the invention.

What is claimed is:
 1. An amplifier, comprising: a plurality ofdifferential pairs coupled together through a common differentialoutput, each differential pair having a current control input; and acurrent switch coupled to the current control input of one of thedifferential pairs to selectively switch said one of the differentialpairs in or out of the amplifier.
 2. The amplifier of claim 1 whereinthe differential pairs each comprises first and second transistorscoupled together through a common a node, the common node comprising thecurrent control input.
 3. The amplifier of claim 2 wherein thetransistors each comprises a field effect transistor
 4. The amplifier ofclaim 3 wherein the first and second transistors in each differentialpair each comprises a source coupled to its respective common node. 5.The amplifier of claim 4 wherein the first and second transistors ineach of the differential pairs each comprises a gate, the gates of thefirst transistors being coupled together and the gates of the secondtransistors being coupled together to form a differential input.
 6. Theamplifier of claim 3 wherein the first and second transistors in each ofthe differential pairs each comprises a drain, the drains of the firsttransistors being coupled together and the drains of the secondtransistors being coupled together to form the differential output. 7.The amplifier of claim 1 wherein the current switch comprises atransistor.
 8. The amplifier of claim 7 wherein the transistor comprisesa field effect transistor.
 9. The amplifier of claim 8 wherein thetransistor comprises a drain coupled to its respective current controlinput.
 10. The amplifier of claim 1 wherein the current switch comprisesa current source having a switch control input.
 11. The amplifier ofclaim 10 further comprising a bias circuit coupled to the switch controlinput.
 12. The amplifier of claim 11 wherein the bias circuit generatesa bias current which is substantially independent of temperature, thebias current being applied to the switch control input.
 13. Theamplifier of claim 12 wherein the bias circuit comprises a first biascircuit having a first bias current exhibiting a positive temperaturecoefficient, a second bias circuit having a second bias currentexhibiting a negative temperature coefficient, and a summer to sum thefirst and second bias currents, the summed first and second biascurrents being applied to the switch control input.
 14. The amplifier ofclaim 13 wherein the summer comprises a cascode current mirror.
 15. Theamplifier of claim 12 wherein the current source comprises a fieldeffect transistor having a gate comprising the switch control input. 16.The amplifier of claim 1 further comprising a matching circuit coupledto the common differential output.
 17. The amplifier of claim 16 whereinthe matching circuit converts a differential current from the commondifferential output to a single-ended current.
 18. The amplifier ofclaim 16 wherein the matching circuit provides an impedancetransformation which is independent of whether said one of thedifferential pairs is switched in or out of the amplifier.
 19. Theamplifier of claim 16 wherein the common differential output comprisesfirst and second outputs, and the matching circuit comprises an inductorhaving a first end coupled to the first output and a capacitor having afirst end coupled to the second output, the inductor and capacitor eachhaving second end coupled together.
 20. The amplifier of claim 1 whereinthe differential pairs are further coupled together through a commondifferential input, the amplifier further comprising an input stagecoupled to the common differential input.
 21. The amplifier of claim 1further comprising a plurality of current switches each coupled to thecurrent control input for a different one of the differential pairs toselectively switch its respective differential pair in or out of theamplifier.
 22. An amplifier, comprising: a plurality of amplifyingstages each having first and second transistors, the first and secondtransistors each having first, second and third nodes, the first nodesof the first transistors being coupled together and the first nodes ofthe second transistors being coupled together to form a differentialoutput, the second nodes of the first transistors being coupled togetherand the second nodes of the second transistors being coupled together toform a differential input, and the third node of each of the firsttransistors being coupled to the third node of its respective secondtransistor to form a current control input for each of the amplifyingstages; and a current switch coupled to the current control input of onethe amplifying stage to switch said one of the amplifying stages in orout of the amplifier.
 23. The amplifier of claim 22 wherein thetransistors each comprises a field effect transistor.
 24. The amplifierof claim 23 wherein the third nodes each comprises a source.
 25. Theamplifier of claim 24 wherein the second nodes each comprises a gate.26. The amplifier of claim 23 wherein the first nodes each comprises adrain.
 27. The amplifier of claim 22 wherein the current switchcomprises a transistor.
 28. The amplifier of claim 27 wherein thetransistor comprises a field effect transistor.
 29. The amplifier ofclaim 28 wherein the transistor comprises a drain coupled to itsrespective current control input.
 30. The amplifier of claim 22 whereinthe current switch comprises a current source having a switch controlinput.
 31. The amplifier of claim 30 further comprising a bias circuitcoupled to the switch control input.
 32. The amplifier of claim 31wherein the bias circuit generates a bias current which is substantiallyindependent of temperature, the bias current being applied the switchcontrol input.
 33. The amplifier of claim 32 wherein the bias circuitcomprises a first bias circuit having a first bias current exhibiting apositive temperature coefficient, a second bias circuit having a secondbias current exhibiting a negative temperature coefficient, and a summerto sum the first and second bias currents, the summed first and secondbias currents being applied to the switch control input.
 34. Theamplifier of claim 33 wherein the summer comprises a cascode currentmirror.
 35. The amplifier of claim 34 wherein the current sourcecomprises a field effect transistor having a gate comprising the switchcontrol input.
 36. The amplifier of claim 22 further comprising amatching circuit coupled to the differential output.
 37. The amplifierof claim 36 wherein the matching circuit converts a differential currentfrom the differential output to a single-ended current.
 38. Theamplifier of claim 36 wherein the matching circuit provides an impedancetransformation which is independent of whether said one of theamplifying stages is switched in or out of the circuit.
 39. Theamplifier of claim 36 wherein the common differential output comprisesfirst and second outputs, and the matching circuit comprises an inductorhaving a first end coupled to the first output and a capacitor having afirst end coupled to the second output, the inductor and capacitor eachhaving second end coupled together.
 40. The amplifier of claim 22further comprising an input stage coupled to the differential input. 41.The amplifier of claim 22 further comprising a plurality of currentswitches each coupled the current control input for a different one ofthe amplifying stages to selectively switch its respective amplifyingstage in or out of the amplifier.
 42. An amplifier, comprising: aplurality of amplifying stages coupled together, each of the amplifyingstages having a current control input; and a current switch coupled tothe current control input of one of the amplifying stages to selectivelyswitch said one of the amplifying stages in or out of the circuit. 43.The amplifier of claim 42 wherein the amplifying stages each comprisesfirst and second transistors coupled together through a common a node,the common node comprising the current control input.
 44. The amplifierof claim 43 wherein the transistors each comprises a field effecttransistor.
 45. The amplifier of claim 44 wherein the first and secondtransistors in each amplifying stage comprises a source coupled to itsrespective common node.
 46. The amplifier of claim 45 wherein the firstand second transistors in each of the amplifying stages each comprises agate, the gates of the first transistors being coupled together and thegates of the second transistors being coupled together to form adifferential input.
 47. The amplifier of claim 44 wherein the first andsecond transistors in each of the differential pairs each comprises adrain, the drains of the first transistors being coupled together andthe drains of the second transistors being coupled together to form adifferential output.
 48. The amplifier of claim 42 wherein the currentswitch comprises a transistor.
 49. The amplifier of claim 48 wherein thetransistor comprises a field effect transistor.
 50. The amplifier ofclaim 49 wherein the transistor comprises a drain coupled to itsrespective current control input.
 51. The amplifier of claim 42 whereinthe current switch comprises a current source having a switch controlinput.
 52. The amplifier of claim 51 further comprising a bias circuitcoupled to the switch control inputs.
 53. The amplifier of claim 52wherein the bias circuit generates a bias current which is substantiallyindependent of temperature, the bias current being applied to the switchcontrol input.
 54. The amplifier of claim 53 wherein the bias circuitcomprises a first bias circuit having a first bias current exhibiting apositive temperature coefficient, a second bias circuit having a secondbias current exhibiting a negative temperature coefficient, and a summerto sum the first and second bias currents, the summed first and secondbias currents being applied to the switch control input.
 55. Theamplifier of claim 54 wherein the summer comprises a cascode currentmirror.
 56. The amplifier of claim 53 wherein the current sourcecomprises a field effect transistor having a gate comprising the switchcontrol input.
 57. The amplifier of claim 42 further comprising amatching circuit coupled to the differential output.
 58. The amplifierof claim 57 wherein the matching circuit converts a differential currentfrom the differential output to a single-ended current.
 59. Theamplifier of claim 57 wherein the matching circuit provides an impedancetransformation which is independent of whether said one of theamplifying stages is switched in or out of the circuit.
 60. Theamplifier of claim 57 wherein the differential output comprises firstand second outputs, and the matching circuit comprises an inductorhaving a first end coupled to the first output and a capacitor having afirst end coupled to the second output, the inductor and capacitor eachhaving second end coupled together.
 61. The amplifier of claim 42wherein the amplifying stages are coupled together to form adifferential input, the amplifier further comprising an input stagecoupled to the differential input.
 62. The amplifier of claim 22 furthercomprising a plurality of current switches each coupled to the currentcontrol input for a different one of the amplifying stages toselectively switch its respective amplifying stage in or out of theamplifier.
 63. An amplifier comprising a digitally programmable powerlevel and a matching circuit which is substantially independent of theprogrammed power level.
 64. The amplifier of claim 63 wherein theamplifier comprises CMOS.
 65. The amplifier of claim 63 furthercomprising a plurality of amplifying stages coupled together, each ofthe amplifying stages having a current control input, and a plurality ofcurrent switches to digitally program the power level of the amplifier,the current switches each being coupled to the current control input fora different one of the amplifying stages to selectively switch itsrespective amplifying stage in or out of the amplifier.
 66. Theamplifier of claim 65 wherein the amplifying stages each comprises firstand second transistors coupled together through a common a node, thecommon node comprising the current control input.
 67. The amplifier ofclaim 66 wherein the transistors each comprises a field effecttransistor.
 68. The amplifier of claim 67 wherein the first and secondtransistors in each amplifying stage comprises a source coupled to itsrespective common node.
 69. The amplifier of claim 68 wherein the firstand second transistors in each of the amplifying stages each comprises agate, the gates of the first transistors being coupled together and thegates of the second transistors being coupled together to form adifferential input.
 70. The amplifier of claim 67 wherein the first andsecond transistors in each of the differential pairs each comprises adrain, the drains of the first transistors being coupled together andthe drains of the second transistors being coupled together to form adifferential output.
 71. The amplifier of claim 65 wherein the currentswitches each comprises a transistor.
 72. The amplifier of claim 71wherein the transistors each comprises a field effect transistor. 73.The amplifier of claim 72 wherein the transistors each comprises a draincoupled to its respective current control input.
 74. The amplifier ofclaim 65 wherein the current switches each comprises a current sourcehaving a switch control input.
 75. The amplifier of claim 74 furthercomprising a plurality of bias circuits each coupled to a different oneof the switch control inputs.
 76. The amplifier of claim 75 wherein thebias circuits each generates a bias current which is substantiallyindependent of temperature, the bias current being applied to itsrespective switch control input.
 77. The amplifier of claim 76 whereinthe bias circuits each comprises a first bias circuit having a firstbias current exhibiting a positive temperature coefficient, a secondbias circuit having a second bias current exhibiting a negativetemperature coefficient, and a summer to sum the first and second biascurrents, the summed first and second bias currents being applied to theits respective switch control input.
 78. The amplifier of claim 77wherein the summer comprises a cascode current mirror.
 79. The amplifierof claim 76 wherein the current sources each comprises a field effecttransistor having a gate comprising the switch control input.
 80. Anamplifier, comprising: a plurality of amplifying stages coupledtogether, switching means for switching one of the amplifying stages inor out of the amplifier to program power of the amplifier; and matchingmeans for matching a load coupled to an output of the amplifier, thematching means being substantially independent of the programmed power.81. The amplifier of claim 80 wherein each of said one of the amplifyingstage comprises first and second transistors coupled together through acommon anode, the common node comprising the current control input. 82.The amplifier of claim 81 wherein the transistors each comprises a fieldeffect transistor.
 83. The amplifier of claim 82 wherein the first andsecond transistors each comprises a source coupled to its respectivecommon node.
 84. The amplifier of claim 83 wherein the amplifying stageseach comprises first and second field effect transistors each having agate, the gates of the first transistors being coupled together and thegates of the second transistors being coupled together to form adifferential input.
 85. The amplifier of claim 82 wherein the amplifyingstages each comprises first and second field effect transistors eachhaving a drain, the drains of the first transistors being coupledtogether and the drains of the second transistors being coupled togetherto form a differential output.
 86. The amplifier of claim 80 wherein theswitching means comprises a transistor.
 87. The amplifier of claim 86wherein the transistor comprises a field effect transistor.
 88. Theamplifier of claim 87 wherein the transistor comprises a drain coupledto said one of the amplifying stages.
 89. The amplifier of claim 80wherein the switching means comprises a current source having a switchcontrol input.
 90. The amplifier of claim 89 further comprising a biascircuit coupled to the switch control input.
 91. The amplifier of claim90 wherein the bias circuit comprises means for generating a biascurrent which is substantially independent of temperature, the biascurrent being applied to the switch control input.
 92. The amplifier ofclaim 90 wherein the bias circuit comprises means for generating a firstbias current exhibiting a positive temperature coefficient, means forgenerating a second bias current exhibiting a negative temperaturecoefficient, and means for summing the first and second bias currents,the summed first and second bias currents being applied to the switchcontrol input.
 93. The amplifier of claim 92 wherein the summercomprises a cascode current mirror.
 94. The amplifier of claim 80wherein the matching means comprises means for converting a differentialcurrent generated by the amplifier stage to a single-ended current, thesingle-ended current being coupled to the amplifier output.
 95. Theamplifier of claim 80 wherein the amplifying stages comprises adifferential output having first and second outputs, and the matchingcircuit comprises an inductor having a first end coupled to the firstoutput and a capacitor having a first end coupled to the second output,the inductor and capacitor each having second end coupled to theamplifier output.